Leddy Maytum Stacy Architects Environmental Noise Study ......Jul 17, 2017 · Commercial To meet...
Transcript of Leddy Maytum Stacy Architects Environmental Noise Study ......Jul 17, 2017 · Commercial To meet...
12 January 2017
Vanna Whitney Leddy Maytum Stacy Architects 677 Harrison Street San Francisco, CA 94107 Email: [email protected]
Subject: 2012 Berkeley Way Apartments Environmental Noise Study
Salter Project: 16-0569
Dear Vanna:
We have conducted an environmental noise study for the project. The purpose of the study is to determine the noise environment at the proposed site, compare measured data with applicable city and state standards, and provide mitigation measures as necessary to meet those standards. This report summarizes the results.
PROJECT CRITERIA
State Noise Standards
Part 1 of the Supplement to the 2016 California Building Code, effective 1 July 2015, requires that the indoor noise level in residential units of multi-family dwellings not exceed DNL1 45 dB where the exterior noise level is greater than DNL 60 dB.
City of Berkeley General P lan
The City General Plan2 has a requirement of DNL 45 dB, which is consistent with the State Standards.
CALGreen
The CALGreen code addresses acoustical issues in several sections. These sections apply to non-residential buildings, which includes the conference rooms, offices, work stations, community room, multipurpose room, commercial kitchen, and meditation/flex room within the building.
1 DNL (Day-Night Average Sound Level) – A descriptor for a 24-hour A-weighted average noise level. DNL accounts for the
increased acoustical sensitivity of people to noise during the nighttime hours. DNL penalizes sound levels by 10 dB during
the hours from 10 PM to 7 AM. For practical purposes, the DNL and CNEL are usually interchangeable. DNL is sometimes
written as Ldn.
2 Note C of the “Land-Use Compatibility for Community Noise Environments” table under Policy EM-47; “Land Use
Compatibility”; Planning and Development Element
2012 Berkeley Way Apartments Environmental Noise Study 12 January 2017 Page 2
Section 5.507.4.3 Acoustical Control
1. There is a requirement for mitigating exterior noise where sound levels regularly exceed 65 dB. If the exterior noise level regularly exceeds 65 dB, then the building envelope must have wall and roof-ceiling assemblies designed to provide an interior noise environment not exceeding an Leq(h)3 of 50 dB in occupied areas during hours of operation.
We assumed that the hours of operation for the commercial spaces would be from 7 am to 10 pm and used the loudest Leq(h) during that period as the basis of design.
NOISE ENVIRONMENT
The proposed 6-story project is located on Berkeley Way between Shattuck Avenue and Milvia Street. The noise environment at the site is predominantly controlled by vehicular traffic along Berkeley Way, with noise from Shattuck Avenue and University Avenue contributing at the higher floors. Berkeley Fire Station No. 2 is located directly across Berkeley Way from the project site, and the associated noise from the fire station (e.g., sirens, horns) contributes to the noise environment, as well.
To quantify the existing noise environment, we conducted three long-term noise measurements between 23 and 27 September 2016 and one 15-minute spot measurement at the project site (see Figure 1 for the measurement locations and measured noise levels). The long-term monitor was at a height of 12 feet above grade. The spot measurement was at a height of 35 feet above grade.
We calculated the noise levels at the various building facades using measured data. A future traffic analysis was not provided for this project. However, we have added 1 dB to the data in our calculations to account for future traffic increases.4
RECOMMENDATIONS
Interior Noise
We calculated the window and exterior door STC5 ratings needed to meet the criteria using the progress drawings received 5 January 2017 that show the floor plans and glazing. Our calculations include the following assumptions:
• Bedrooms, dorms, shelters, work spaces, and offices will have carpet • All other rooms will have hard-surfaced flooring • Ceilings are 9-feet high
3 Leq(h) – The equivalent steady-state A-weighted sound level that, in an hour, would contain the same acoustic energy as
the time-varying sound level during the same hour.
4 The California Department of Transportation assumes a traffic volume increase of three-percent per year, which
corresponds to a 1 dB increase in DNL over a ten-year period.
5 STC (Sound Transmission Class) – A single-number rating defined in ASTM E90 that quantifies the airborne sound insulating
performance of a partition under laboratory conditions. Increasing STC ratings correspond to improved airborne sound
insulation.
2012 Berkeley Way Apartments Environmental Noise Study 12 January 2017 Page 3
• Window sizes and locations are as shown on the floor plans and elevations • The exterior facade will be HardiePanel, Lap Siding, or a premium fiber cement board panel
The recommended STC ratings are for full window assemblies (glass and frame) rather than just the glass itself. Tested, sound-rated assemblies should be used.
For reference, typical one-inch glazing assemblies (two 1/4-inch thick panes with a 1/2-inch airspace) can achieve an STC rating of 28 depending on the window type and manufacturer.
To meet the indoor DNL 45 dB criterion, it will be necessary for all of the windows in the facades to be sound-rated. The window and exterior door STC ratings will need to be as shown on Figures 2 through 6.
Where windows need to be closed to achieve an indoor DNL of 45 dB, an alternative method of supplying fresh air (e.g., mechanical ventilation) should be considered. This applies to the entire project and should be discussed with the project mechanical engineer.
Commercial
To meet the CALGreen interior noise criterion of Leq(h) 50 dB, the glazing system STC ratings for the commercial space will need to be as shown on Figures 2, 3 and 6.
* * *
This concludes our environmental noise study for the 2012 Berkeley Way project. Should you have any questions, please give us a call.
Sincerely,
CHARLES M. SALTER ASSOCIATES, INC.
Blake Wells, LEED® Green Associate Jason R. Duty, PE Consultant Vice President Enclosures as noted
Tree Assessment Map 2012 Berkeley Way Berkeley, CA Prepared for: Bridge Housing Corporation San Francisco, CA February 2017 No Scale Notes Base map provided by: Sandis Oakland, CA Numbered tree locations are approximate.
325 Ray Street Pleasanton, California 94566 Phone 925.484.0211 Fax 925.484.0596
94 95 96 97 98
99
100 101 102 103
TREE SPECIES SIZE CONDITION SUITABILITY COMMENTSNo. DIAMETER 1=POOR FOR
(in inches) 5=EXCELLENT PRESERVATION
94 Coast live oak 8,6,5 2 Low Poor form and structure; stem removed E.; one sided W.; twig dieback.
95 Coast live oak 12,9,9 2 Low Multiple attachments at 4'; seam in attachments; moderate dieback; cracked curb S.
96 Coast live oak 10 3 Low Multiple attachments at 6'; sweeps W. from base; basal wounds; twig dieback.
97 Coast live oak 17 3 Moderate Multiple attachments at 5'; good form; twig dieback; displacing sidewalk 2"; almost outgrown 3' planter strip.
98 Coast live oak 12 3 Low Multiple attachments at 8'; fair form and structure; basal wound/grown over & cracked curb S.
99 Coast redwood 36 2 Low Topped at 60' with crooks in trunk above; extensive dieback w/ dead branches to 3"; engulfed in vines.
100 Coast live oak 10,9,5,4 2 Low Off-site, no tag; multiple attachments at 2'; growing through/embedded chain link dance; in very narrow planting strip.
101 Coast live oak 8,7,7,6 2 Low Off-site, no tag; codominant trunks at base; growing through/embedded chain link fence; in very narrow planting strip.
102 Coast live oak 17 3 Moderate Off-site, no tag; codominant trunks at 10'; grown around/embedded pipe at 1'; in small planter.
103 Buckeye 13,11,9,8,4 4 Moderate Off-site, no tag; multiple attachments at 3'; growing against retaining wall; in very narrow planting strip.
Tree Assessment Berkeley WayBerkeley CaliforniaFebruary 2017
Page 1
Prepared for BRIDGE Housing Corporation
GEOTECHNICAL INVESTIGATION PROPOSED MIXED-USE BUILDING
2012 BERKELEY WAY Berkeley, California
UNAUTHORIZED USE OR COPYING OF THIS DOCUMENT IS STRICTLY PROHIBITED BY ANYONE OTHER THAN THE CLIENT FOR THE SPECIFIC PROJECT
March 27, 2017 Project No. 16-1193
March 27, 2017 Project No. 16-1193
Mr. Jamie Hiteshew BRIDGE Housing Corporation 600 California Street, Suite 900 San Francisco, CA 94108
Subject: Geotechnical Investigation Report Proposed Mixed-Use Building 2012 Berkeley Way Berkeley, California
Dear Mr. Hiteshew:
We are pleased to present the results of our geotechnical investigation for the proposed mixed-use building to be constructed at 2012 Berkeley Way in Berkeley, California. Our services were provided in accordance with our proposal dated September 8, 2016.
The project site is located on the south side of Berkeley Way between Shattuck Avenue and Milvia Street, approximately 200 feet west of its intersection with Shattuck Avenue. The project site consists of a rectangular-shaped parcel with plan dimensions of approximately 110 by 320 feet. The site is currently an asphalt-paved parking lot that is owned by the City of Berkeley.
BRIDGE Housing (BRIDGE) in partnership with Berkeley Food and Housing Project (BFHP) plans to construct a mixed-use building at the site. The proposed building will consist of five stories of wood-framed construction (Type III construction) over two levels of reinforced concrete podium (Type 1 construction). The lower podium level will be below-grade and will consist of replacement public parking; park lifts may be installed at the below-grade parking level to achieve a greater number of parking spaces. Above the garage, the BRIDGE and BFHP spaces will be separated by a demising wall and will have separate vertical circulation systems (i.e. exit stairs and elevators) on each side of the demising wall. On the BRIDGE side, there will be 94 units of affordable residential rental housing for families, as well as shared community amenities such as community rooms. On the BFHP side, there will be emergency homeless shelter rooms, transitional housing rooms, studios for permanently supportive housing, supportive services, administrative offices, reception area, conference rooms, computer rooms, community and multipurpose space, commercial kitchen, storage, laundry, and flexible spaces.
From a geotechnical standpoint, we conclude the site can be developed as planned, provided the recommendations presented in our report are incorporated into the project plans and specifications and implemented during construction. The primary geotechnical
Mr. Jamie Hiteshew BRIDGE Housing Corporation March 27, 2016 Page 2 concerns at the site are: 1) a design groundwater level that is near the proposed finished floor of the below-grade level, 2) providing adequate foundation support, and 3) providing lateral support for the proposed excavation while minimizing the impact on the surrounding improvements. We conclude the proposed building may be supported on spread footings or a mat foundation. Where basement slab will extend below the design groundwater level, a under slab drainage system should be installed to reduce hydrostatic pressures. Alternatively, the floor slab/mat should be waterproofed and the foundations be designed to resist hydrostatic pressures.
Our report contains specific recommendations regarding earthwork and grading, foundation design, shoring, and other geotechnical issues. The recommendations contained in our report are based on limited subsurface exploration. Consequently, variations between expected and actual soil conditions may be found in localized areas during construction. Therefore, we should be engaged to observe foundation installation, grading, shoring installation, and fill placement, during which time we may make changes in our recommendations, if deemed necessary.
We appreciate the opportunity to provide our services to you on this project. If you have any questions, please call.
Sincerely yours, ROCKRIDGE GEOTECHNICAL, INC.
Darcie Maffioli, P.E. Linda H. J. Liang, P.E., G.E. Project Engineer Associate Engineer
Enclosure
QUALITY CONTROL REVIEWER:
Craig S. Shields, P.E., G.E. Principal Engineer
TABLE OF CONTENTS
1.0 INTRODUCTION ...............................................................................................................1
2.0 SCOPE OF SERVICES .......................................................................................................2
3.0 FIELD INVESTIGATION AND LABORATORY TESTING ...........................................3 3.1 Test Borings .............................................................................................................3 3.2 Laboratory Testing ...................................................................................................4
4.0 SITE AND SUBSURFACE CONDITIONS .......................................................................5 4.1 Site Conditions .........................................................................................................5 4.2 Subsurface Conditions .............................................................................................6 4.3 Groundwater ............................................................................................................7
5.0 SEISMIC CONSIDERATION ............................................................................................8 5.1 Regional Seismicity and Faulting ............................................................................8 5.2 Geologic Hazards ...................................................................................................12
5.2.1 Ground Shaking .........................................................................................12 5.2.2 Liquefaction and Associated Hazards ........................................................12 5.2.3 Cyclic Densification ...................................................................................13 5.2.4 Fault Rupture .............................................................................................13
6.0 DISCUSSIONS AND CONCLUSIONS ...........................................................................14 6.1 BART Subway Zone-of-Influence .........................................................................14 6.2 Design Groundwater Level ....................................................................................15 6.3 Foundations and Settlement ...................................................................................15 6.4 Underpinning .........................................................................................................16 6.5 Temporary Cut Slope and Shoring ........................................................................17 6.6 Excavation Dewatering ..........................................................................................19 6.7 Excavation, Monitoring, and Construction Considerations ...................................19 6.8 Soil Corrosivity ......................................................................................................20
7.0 RECOMMENDATIONS ...................................................................................................21 7.1 Site Preparation and Grading .................................................................................21
7.1.1 Soil Subgrade Preparation..........................................................................21 7.1.2 Soil Subgrade Stabilization ........................................................................22 7.1.3 Fill Materials and Compaction Criteria .....................................................24 7.1.4 Utility Trench Backfill ...............................................................................25 7.1.5 Exterior Flatwork Subgrade Preparation ...................................................26
7.2 Foundations ............................................................................................................26 7.2.1 Spread Footings .........................................................................................26 7.2.2 Mat Foundation ..........................................................................................27
7.3 Underslab Drainage System ...................................................................................28
7.4 Slab-on-Grade Floor ..............................................................................................29 7.5 Permanent Below-Grade Walls ..............................................................................31 7.6 Underpinning .........................................................................................................32 7.7 Temporary Cut Slopes and Shoring .......................................................................33
7.7.1 Cantilevered Soldier Pile and Lagging Shoring .........................................34 7.7.2 Soldier Pile and Lagging Shoring System with Tiebacks ..........................35 7.7.3 Soil-Nail Shoring System ..........................................................................38
7.8 Seismic Design.......................................................................................................40
8.0 GEOTECHNICAL SERVICES DURING CONSTRUCTION ........................................40
9.0 LIMITATIONS ..................................................................................................................41 REFERENCES
FIGURES
APPENDIX A – Logs of Borings
APPENDIX B – Laboratory Test Results
LIST OF FIGURES
Figure 1 Site Location Map
Figure 2 Site Plan
Figure 3 Generalized Cross Section A-A’ Zone of Influence for BART Subway Structures
Figure 4 Regional Fault Map
Figure 5 Regional Geologic Map
Figure 6 Seismic Hazards Zone Map
Figure 7 Design Parameters for Soldier-Pile-and-Lagging Temporary Shoring System
APPENDIX A
Figures A-1 Logs of Borings B-1 through and A-5 and B-5
Figure A-6 Classification Chart
APPENDIX B
Figure B-1 Plasticity Chart
Figure B-2 Particle Size Distribution
Figures B-3 Unconsolidated-Undrained Triaxial Compression and B-4 Test Reports
Corrosivity Analysis Results
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GEOTECHNICAL INVESTIGATION PROPOSED MIXED-USE BUILDING
2012 BERKLEY WAY Berkeley, California
1.0 INTRODUCTION
This report presents the results of the geotechnical investigation performed by Rockridge
Geotechnical, Inc. for the proposed mixed-use building to be constructed at 2012 Berkeley Way
in Berkeley, California. The project site is located on the southern side of Berkeley Way
between Shattuck Avenue and Milvia Street, approximately 200 feet west of its intersection with
Shattuck Avenue, as shown on the Site Location Map, Figure 1.
The project site consists of a rectangular-shaped parcel with plan dimensions of approximately
110 by 320 feet as shown on the Site Plan, Figure 2. The site is currently an asphalt-paved
parking lot that is owned by the City of Berkeley. Existing site grades slope down gently to the
southwest from about Elevation 196 feet1 at the northeastern corner to Elevation 192 feet at the
southwestern corner. The site is bordered by Berkeley Way to the north, single-story
commercial buildings to the east, one- to three-story commercial buildings to the south, and two-
story residential buildings to the west.
BRIDGE Housing (BRIDGE) in partnership with Berkeley Food and Housing Project (BFHP)
plans to construct a mixed-use building at the site. The proposed building will consist of five
stories of wood-framed construction (Type III construction) over two levels of reinforced
concrete podium (Type 1 construction). The lower podium level will be below-grade and will
consist of replacement public parking; park lifts may be installed at the below-grade parking
level to achieve a greater number of parking spaces. Above the garage, the BRIDGE and BFHP
spaces will be separated by a demising wall and will have separate vertical circulation systems
(i.e. exit stairs and elevators) on each side of the demising wall. On the BRIDGE side, there will
be 94 units of affordable residential rental housing for families, as well as shared community
1 Unless otherwise noted, elevations in this report are based on topographic information shown on the
drawing titled “Topographic Survey,” prepared by Sandis, revised January 26, 2017, City of Berkeley Datum.
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amenities such as community rooms. On the BFHP side, there will be emergency homeless
shelter rooms, transitional housing rooms, studios for permanently supportive housing,
supportive services, administrative offices, reception area, conference rooms, computer rooms,
community and multipurpose space, commercial kitchen, storage, laundry, and flexible spaces.
2.0 SCOPE OF SERVICES
Our geotechnical investigation was performed in accordance with our proposal dated
September 8, 2016. Our scope of services consisted of evaluating subsurface conditions at the
site by drilling five test borings, performing laboratory testing on selected soil samples collected
from the borings, and performing engineering analyses to develop conclusions and
recommendations regarding:
subsurface conditions
site seismicity and seismic hazards, including the potential for liquefaction and lateral spreading, and total and differential settlement resulting from liquefaction and/or cyclic densification
BART subway zone-of-influence
the most appropriate foundation type(s) for the proposed building
design criteria for the recommended foundation type(s), including vertical and lateral capacities for each of the foundation type(s)
estimates of foundation settlement
lateral earth pressures for basement walls
temporary shoring
underpinning
temporary and permanent dewatering
site preparation and grading, including criteria for fill quality and compaction
slab-on-grade floors
2016 California Building Code site class and design spectral response acceleration parameters
corrosivity of the near-surface soil and the potential effects on buried concrete and metal structures and foundations
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construction considerations
3.0 FIELD INVESTIGATION AND LABORATORY TESTING
Subsurface conditions at the site were investigated by drilling five borings and performing
laboratory testing on selected soil samples. Prior to our field investigation, we obtained a
drilling permit from the City of Berkeley, Planning and Development Department, Toxic
Management Division (CBTMD), and contacted Underground Service Alert (USA) to notify
them of our work, as required by law. We also retained a private utility locator, Precision
Locating, LLC, to check that boring locations were clear of underground utilities. Details of the
field investigation and laboratory testing are described in the remainder of this section.
3.1 Test Borings
Five borings were drilled on September 29 and 30, 2016 by Exploration Geoservices, Inc. of San
Jose, California at the approximate locations shown on Figure 2. The borings, designated B-1
through B-5, were drilled to depths between 39 and 50 feet below the existing ground surface
(bgs) using a Mobile B-53 drill rig equipped with hollow-stem augers. During drilling, our field
engineer logged the soil encountered and obtained samples for visual classification and
laboratory testing. The boring logs were developed based on soil conditions observed and
logged by our field engineer during drilling, review of soil samples in the office to confirm
classification, and the results of laboratory tests on selected soil samples. Logs of the borings are
presented in Appendix A on Figures A-1 through A-5. The soil encountered in the borings was
classified in accordance with the classification chart shown on Figure A-6.
Soil samples were obtained using the following samplers:
Sprague and Henwood (S&H) split-barrel sampler with a 3.0-inch outside diameter and 2.5-inch inside diameter, lined with 2.43-inch inside diameter stainless steel tubes
Standard Penetration Test (SPT) split-barrel sampler with a 2.0-inch outside and 1.5-inch inside diameter, without liners.
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The type of sampler used was selected based on soil type and the desired sample quality for
laboratory testing. In general, the S&H sampler was used to obtain samples in medium stiff to
very stiff cohesive soil and the SPT sampler was used to evaluate the relative density of sandy
soil.
The samplers were driven with a 140-pound, downhole safety hammer falling about 30 inches
per drop. The samplers were driven up to 18 inches and the hammer blows required to drive the
samplers were recorded every six inches and are presented on the boring logs. A “blow count” is
defined as the number of hammer blows per six inches of penetration or 50 blows for six inches
or less of penetration. The blow counts used for this conversion were: (1) the last two blow
counts if the sampler was driven more than 12 inches, or (2) the only blow count if the sampler
was driven six inches or less. The blow counts required to drive the S&H and SPT samplers
were converted to approximate SPT N-values using factors of 0.7 and 1.2, respectively, to
account for sampler type and approximate hammer energy, as well as the fact that the SPT
sampler was used without liners, but could accommodate liners. The converted SPT N-values
are presented on the boring logs.
Upon completion of drilling, the boreholes were backfilled with cement grout under the
observation of the CBTMD grout inspector and topped with concrete. The soil cuttings
generated by the borings were collected in drums. The soil drums were removed from the site at
the completion of drilling and subsequently disposed of in a non-hazardous waste disposal
facility.
3.2 Laboratory Testing
We re-examined each soil sample obtained from our borings to confirm the field classifications
and selected representative samples for laboratory testing. Geotechnical laboratory tests were
performed on selected soil samples to assess their engineering properties and physical
characteristics. Soil samples were tested by B. Hillebrandt Soils Testing, Inc. of Alamo,
California to measure moisture content, dry density, percent passing the No. 200 sieve, plasticity
(Atterberg limits), and strength. Corrosivity testing of two samples of near-surface soil was
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performed by Sunland Analytical of Rancho Cordova, California. The results of the
geotechnical laboratory tests are presented on the boring logs and in Appendix B.
4.0 SITE AND SUBSURFACE CONDITIONS
This section summarizes the site and subsurface conditions at 2012 Berkeley Way based on the
results of this investigation, published geologic data, and subsurface information collected from
other projects in the vicinity. Site-specific descriptions of the site, subsurface soil, and
groundwater conditions are presented below.
4.1 Site Conditions
The site is currently occupied by an asphalt-paved parking lot owned by the City of Berkeley.
Existing site grades slope down gently to the southwest from about Elevation 196 feet2 at the
northeastern corner to Elevation 192 feet at the southwestern corner.
Three single-story commercial buildings are located to the east of the site. The single-story
structure abutting the northeastern corner of the site is at a similar elevation as the parking lot.
The other single-story structures to the east are founded at a gradually lower elevation toward the
intersection of Shattuck and University avenues.
There is a retaining wall along the southern property line and the top of wall is at the current site
(parking lot) grade. The site is bordered by five one- to three-story commercial buildings to the
south, as shown on Figure 2. There are three pedestrian entrances to some of the commercial
building from the City of Berkeley parking lot. Topographic Survey, prepared by Sandis and last
revised January 26, 2017, indicates two of the buildings are built up to the southern property line
and three of the buildings are set-back about 4, 14, and 19-1/2 feet from the southern property
line.
2 Unless otherwise noted, elevations in this report are based on topographic information shown on the
drawing titled “Topographic Survey,” prepared by Sandis, revised January 26, 2017, City of Berkeley Datum.
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Two 2-story residential buildings are located to the west of the site. The locations of these
buildings are shown in the aerial photo on Figure 2. We do not have information regarding the
foundations of these buildings but anticipate that they are supported on shallow foundations.
Topographic Survey, prepared by Sandis and last revised January 26, 2017, indicates there is a
driveway, about 12 feet wide, between the western property line and these residential buildings.
There is a San Francisco Bay Area Rapid Transit (BART) subway below Shattuck Avenue that
crosses the block to the north of the project site diagonally. The approximate alignment of the
BART right-of-way near the project site is shown on Figure 2. New construction located within
the BART subway’s zone-of-influence (ZOI), defined as a line extending upward at an
inclination of 1.5:1 (horizontal: vertical) from the base of the subway, will require measures to
be taken to avoid surcharging the subway structure. On November 1, 2016, we reviewed as-built
documents for the Berkeley-Richmond line near the site at the BART office in Oakland. Based
on the as-built documents we obtained from BART, the subway right-of-way is located about
38 feet northeast of the northeastern corner of the site and the base of the subway is about 42 feet
bgs. A generalized cross section showing the approximate location and depth of the BART
subway and the ZOI is presented on Figure 3.
4.2 Subsurface Conditions
As presented on the Regional Geologic Map (Figure 4), the site is underlain by Holocene-age
alluvial fan and fluvial deposits (Qhaf) (Graymer, 2000). Alluvial and fluvial deposits are
sediments deposited by rivers and streams.
The results of our borings indicate the site is underlain by medium stiff to hard clay with varying
sand and gravel content interbedded with occasional layers of medium dense to very dense
clayey sand to the maximum depth explored of 39 to 50 feet bgs. Generally, the sands and
gravels have moderate to high fines (clay and silt) content.
Two Atterberg limits tests were performed on selected samples of the near-surface clay (i.e.,
upper 1-1/2 to 3 feet) obtained from Borings B-3 and B-4. The Atterberg limits test results
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indicate the samples tested have plasticity indices (PI) of 16 and 21, which indicate the surficial
soil has moderate expansion potential3.
4.3 Groundwater
Groundwater was encountered during drilling in Borings B-3, B-4, and B-5. Groundwater was
measured at a depth of about 21 feet bgs in Boring B-3 after leaving the borehole open for about
three hours after completion of drilling. Groundwater was measured in Borings B-4 and B-5 at
depths of about 38 and 43 feet bgs, respectively, immediately following the completion of
drilling. The groundwater level measurements in Borings B-3, B-4, and B-5 were taken
immediately or shortly after completion of drilling and may not reflect stabilized groundwater
levels. The groundwater level at the site is expected to fluctuate several feet seasonally with
potentially larger fluctuations annually, depending on the amount of rainfall. Although this past
winter was not particularly dry, rainfall during the previous few winters has been well below
normal and, therefore, our groundwater readings likely do not reflect the high groundwater levels
following winters with above-normal rainfall.
To help estimate the highest potential groundwater level at the site, we reviewed data collected at
a nearby development for the University of California, Berkeley (UCB) and information on the
State of California Water Resources Control Board GeoTracker website
(http://geotracker.waterboards.ca.gov/).
To the east of the site, A3GEO performed a geotechnical study for UCB for the development
located on the northeastern corner of Shattuck Avenue and Berkeley Way. Twelve borings were
drilled using hollow-stem augers at the site. During drilling, groundwater was recorded at depths
ranging from 16 to 31 feet bgs about 15 to 40 minutes following the completion of drilling; we
judge these readings do not represent stabilized groundwater levels because there was
insufficient time for the groundwater to stabilize. One boring (Boring B-10 located about
170 feet east of Shattuck Avenue and 40 feet north of Berkeley Way) was converted to a
3 Expansive soil undergoes volumetric changes with changes in moisture content (i.e. it shrinks when
dried and swells when wetted).
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piezometer after drilling. Between August 2009 and January 2010, groundwater was measured
in the piezometer on four occasions at depths ranging from 11-1/2 to 14-1/2 feet bgs (A3GEO,
2015).
Several nearby sites with historical groundwater data on the GeoTracker website include
1929 University Avenue, which is approximately 700 feet southwest of the site, and 2009, 2011,
and 2015 Addison Street, which is approximately 700 feet south of the site. Data from 1929
University Avenue indicates that the depth to stabilized groundwater is about 18 feet bgs
(Schultze & Associates, Inc., 2013). The highest groundwater level measured at the Addison
Street site between October 1991 and August 1994 was at a depth of 13.4 feet bgs (Subsurface
Consultants, Inc., 1994). The ground surface elevation at these two locations is approximately
20 feet lower than the subject site. Based on this data, the groundwater flow direction appears to
be towards the south-southwest direction.
Considering the above groundwater data and the fact that our recent investigation was performed
following several years of drought, we conclude a design groundwater depth of 12 feet bgs
should be used for design of the proposed building.
5.0 SEISMIC CONSIDERATION
The results of our evaluation regarding seismic considerations for the project site are presented in
the following sections.
5.1 Regional Seismicity and Faulting
The site is located in the Coast Ranges geomorphic province of California that is characterized
by northwest-trending valleys and ridges. These topographic features are controlled by folds and
faults that resulted from the collision of the Farallon plate and North American plate and
subsequent strike-slip faulting along the San Andreas Fault system. The San Andreas Fault is
more than 600 miles long from Point Arena in the north to the Gulf of California in the south.
The Coast Ranges province is bounded on the east by the Great Valley and on the west by the
Pacific Ocean.
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The major active faults in the area are the Hayward, Calaveras, San Andreas, and San Gregorio.
These and other faults in the region are shown on Figure 5. For these and other active faults
within a 50-kilometer radius of the site, the distance from the site and estimated mean
characteristic Moment magnitude4 [2007 Working Group on California Earthquake Probabilities
(WGCEP) (USGS 2008) and Cao et al. (2003)] are summarized in Table 1.
4 Moment magnitude is an energy-based scale and provides a physically meaningful measure of the
size of a faulting event. Moment magnitude is directly related to average slip and fault rupture area.
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TABLE 1 Regional Faults and Seismicity
Fault Segment Approximate Distance from
Site (km)
Direction from Site
Mean Characteristic
Moment Magnitude
Total Hayward 1.3 Northeast 7.0
Total Hayward-Rodgers Creek 1.3 Northeast 7.3
Mount Diablo Thrust 20 East 6.7
Green Valley Connected 23 East 6.8
Total Calaveras 24 East 7.0
N. San Andreas - Peninsula 28 West 7.2
N. San Andreas (1906 event) 28 West 8.1
Rodgers Creek 28 Northwest 7.1
N. San Andreas - North Coast 28 West 7.5
West Napa 33 North 6.7
San Gregorio Connected 33 West 7.5
Greenville Connected 38 East 7.0
Great Valley 5, Pittsburg Kirby Hills 41 East 6.7
Monte Vista-Shannon 48 South 6.5
Since 1800, four major earthquakes have been recorded on the San Andreas Fault. In 1836, an
earthquake with an estimated maximum intensity of VII on the Modified Mercalli (MM) scale
occurred east of Monterey Bay on the San Andreas Fault (Toppozada and Borchardt, 1998).
The estimated Moment magnitude, Mw, for this earthquake is about 6.25. In 1838, an earthquake
occurred with an estimated intensity of about VIII-IX (MM), corresponding to a Mw of about 7.5.
The San Francisco Earthquake of 1906 caused the most significant damage in the history of the
Bay Area in terms of loss of lives and property damage. This earthquake created a surface
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rupture along the San Andreas Fault from Shelter Cove to San Juan Bautista approximately
470 kilometers in length. It had a maximum intensity of XI (MM), a Mw of about 7.9, and was
felt 560 kilometers away in Oregon, Nevada, and Los Angeles. The most recent earthquake to
affect the Bay Area was the Loma Prieta Earthquake of October 17, 1989, with a Mw of 6.9.
This earthquake occurred in the Santa Cruz Mountains about 99 kilometers southwest of the site.
In 1868, an earthquake with an estimated maximum intensity of X on the MM scale occurred on
the southern segment (between San Leandro and Fremont) of the Hayward Fault. The estimated
Mw for the earthquake is 7.0. In 1861, an earthquake of unknown magnitude (probably a Mw of
about 6.5) was reported on the Calaveras Fault. The most recent significant earthquake on this
fault was the 1984 Morgan Hill earthquake (Mw = 6.2).
The U.S. Geological Survey's 2014 Working Group on California Earthquake Probabilities has
compiled the earthquake fault research for the San Francisco Bay area in order to estimate the
probability of fault segment rupture. They have determined that the overall probability of
moment magnitude 6.7 or greater earthquake occurring in the San Francisco Region during the
next 30 years (starting from 2014) is 72 percent. The highest probabilities are assigned to the
Hayward Fault, Calaveras Fault, and the northern segment of the San Andreas Fault. These
probabilities are 14.3, 7.4, and 6.4 percent, respectively.
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5.2 Geologic Hazards
Because the project site is in a seismically active region, we evaluated the potential for
earthquake-induced geologic hazards including ground shaking, ground surface rupture,
liquefaction,5 lateral spreading,6 and cyclic densification7. We used the results of our field
investigation to evaluate the potential of these phenomena occurring at the project site.
5.2.1 Ground Shaking
The seismicity of the site is governed by the activity of the Hayward Fault, although ground
shaking from future earthquakes on other faults, including the San Andreas, Calaveras, and San
Gregorio faults, will also be felt at the site. The intensity of earthquake ground motion at the site
will depend upon the characteristics of the generating fault, distance to the earthquake epicenter,
and magnitude and duration of the earthquake. The site is less than two kilometers from the
Hayward Fault. We judge that strong to very strong ground shaking could occur at the site
during a large earthquake on one of the nearby faults.
5.2.2 Liquefaction and Associated Hazards
When a saturated, cohesionless soil liquefies, it experiences a temporary loss of shear strength
created by a temporary rise in excess pore pressure generated by strong ground motion. Soil
susceptible to liquefaction includes loose to medium dense sand and gravel, low-plasticity silt,
and some low-plasticity clay deposits. Flow failure, lateral spreading, differential settlement,
loss of bearing strength, ground fissures and sand boils are evidence of excess pore pressure
generation and liquefaction.
5 Liquefaction is a phenomenon where loose, saturated, cohesionless soil experiences temporary
reduction in strength during cyclic loading such as that produced by earthquakes. 6 Lateral spreading is a phenomenon in which surficial soil displaces along a shear zone that has
formed within an underlying liquefied layer. Upon reaching mobilization, the surficial blocks are transported downslope or in the direction of a free face by earthquake and gravitational forces.
7 Cyclic densification is a phenomenon in which non-saturated, cohesionless soil is compacted by earthquake vibrations, causing ground-surface settlement.
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The site is not located within an area of Berkeley that is designated as a potential liquefaction
hazard zone on the map prepared by CGS titled State of California, Seismic Hazard Zones,
Oakland West Quadrangle, Official Map, dated February 14, 2003 (Figure 6). We evaluated the
liquefaction potential of soil encountered below groundwater at the site using data collected in
our borings. Considering the soil encountered in our borings below the design groundwater level
(12 feet bgs) generally consists of very stiff to hard clay and dense clayey sand, we judge the soil
is not susceptible to liquefaction because of its cohesion or high relative density. Therefore, we
conclude the potential for liquefaction to occur at the site is very low.
5.2.3 Cyclic Densification
Cyclic densification (also referred to as differential compaction) of non-saturated sand (sand
above groundwater table) can occur during an earthquake, resulting in settlement of the ground
surface and overlying improvements.
The results of our borings indicate the soil above the groundwater at the site generally consists of
cohesive soil, interbedded with relatively dense granular soil, which are not susceptible to cyclic
densification due to its relatively high fines content and high density. Therefore, we conclude
the potential for ground surface settlement resulting from cyclic densification at the site is very
low.
5.2.4 Fault Rupture
Historically, ground surface displacements closely follow the trace of geologically young faults.
The site is not within an Earthquake Fault Zone, as defined by the Alquist-Priolo Earthquake
Fault Zoning Act, and no known active or potentially active faults exist on the site. We,
therefore, conclude the risk of fault offset at the site from a known active fault is very low. In a
seismically active area, the remote possibility exists for future faulting in areas where no faults
previously existed; however, we conclude the risk of surface faulting and consequent secondary
ground failure from previously unknown faults is also very low.
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6.0 DISCUSSIONS AND CONCLUSIONS
From a geotechnical standpoint, we conclude the site can be developed as planned, provided the
recommendations presented in this report are incorporated into the project plans and
specifications and implemented during construction. The primary geotechnical concerns at the
site are: 1) a design groundwater level that is near the proposed finished floor of the below-grade
level, 2) providing adequate foundation support, and 3) providing lateral support for the
proposed excavation while minimizing the impact on the surrounding improvements. These and
other geotechnical issues, as they pertain to the proposed development, are discussed in the
remainder of this section.
6.1 BART Subway Zone-of-Influence
As discussed above in Section 4.1, the BART subway right-of-way is located about 38 feet
northeast of the northeastern corner of the site and the bottom of the subway is about 42 feet bgs.
As shown on Figure 3, the BART ZOI line daylights about 13 feet inside the subject property
and the bottom of the ZOI is approximately 9 feet bgs at the northeastern corner of the site. The
BART guidelines state that “all structures shall be designed as not to impose any temporary or
permanent adverse effects including unbalanced loading and seismic loading, on the adjacent
BART subways”. Considering the proposed building will have one basement level that will
extend about 12 feet bgs (depending on foundation thickness), we anticipate the foundations for
the proposed building will derive support below the ZOI and will not impose any temporary or
permanent loads on the BART subway.
The BART guidelines also state that temporary shoring located within the ZOI “shall be required
to maintain at-rest soil condition and monitored for movement.” Therefore, temporary shoring
system along the eastern property line and within 50 feet horizontally from the BART right-of-
way should be designed for at-rest soil conditions. Although the BART guidelines do not state
installation of tiebacks is prohibited within the ZOI, it is our experience that tiebacks will not be
allowed with this zone.
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6.2 Design Groundwater Level
Based on the existing and historical groundwater level data presented in Section 4.3, we
conclude a groundwater depth of 12 feet bgs should be used for design. A permanent dewatering
system (underslab drainage system), as presented in Section 7.3, may be installed to reduce
hydrostatic pressures on floor slabs, basement walls, and building foundations. Alternatively, the
basement walls, building foundations, and mat/floor slabs extending below the design
groundwater level can be waterproofed and designed to resist hydrostatic pressures.
6.3 Foundations and Settlement
The moderately expansive near-surface clay at the site is subject to volume changes during
seasonal fluctuations in moisture content. These volume changes can cause cracking of
foundations and floor slabs supported on the clay. Considering the finished floor for the
basement level in the proposed building will be founded well below the depth where seasonal
moisture changes in the soil occurs, mitigation measures to address the potential adverse impacts
of the moderately expansive near-surface soil on slabs and foundations are not required.
The foundation level of the proposed building with a basement will be underlain by stiff to hard
clay that can support moderate building loads. From a geotechnical standpoint, the proposed
building may be supported on shallow foundations consisting of conventional spread footings or
a mat foundation. Where basement slab/mat will extend below the design groundwater level, an
underslab drainage system should be installed to reduce hydrostatic pressures.
Recommendations for an underslab drainage system are presented in Section 7.3. Alternatively,
the floor slab/mat can be waterproofed and the foundations designed to resist hydrostatic
pressures.
We estimate total and differential settlement of properly constructed spread footings or mat
foundation designed using the recommendations presented in Section 7.2 of this report will be
less than one inch and 1/2 inch over a 30-foot horizontal distance, respectively.
The presence of adjacent buildings should be taken into account when designing foundations for
the proposed building to avoid surcharging the adjacent below-grade walls or foundations. It
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will be necessary to determine the configuration and depth of adjacent below-grade walls and
foundations. If as-built plans cannot be obtained, test pits should be excavated prior to
construction to determine adjacent below-grade wall depth, if any, and foundation type and
depth, as appropriate.
6.4 Underpinning
Underpinning of neighboring structures may be needed if excavations will be adjacent to and
extend below the elevation of the bottom of the foundations for adjacent structures. To
determine the need for underpinning and, if underpinning is needed, to provide information for
design of the underpinning system, it will be necessary to determine the configuration and depth
of existing foundations that bottom above an imaginary line extending up at an inclination of
1.5:1 from proposed excavations. If as-built plans cannot be obtained, test pits should be
excavated prior to construction to determine the foundation type and depth to complete the
design of an appropriate underpinning system. We can evaluate the extent of underpinning
required once the location of new foundation elements relative to existing foundations is
determined.
We conclude the most appropriate underpinning method would be hand-excavated end-bearing
piers. Hand-excavated, end bearing piers are generally installed by excavating three-foot by
five-foot rectangular shafts a minimum of two feet below the proposed basement excavation
depth, installing reinforcing steel, and backfilling with structural concrete. The shafts are
constructed in incremental phases to maintain support for the existing foundation. Each shaft is
shored with timber as it is excavated. The cut between adjacent shafts can be shored with timber
lagging as the excavation proceeds.
Where underpinning will extend relatively deep, it may be more economical to use slant drilled
cast-in-place soldier piles. This alternative should be further evaluated once the elevation of
adjacent foundations is known.
Underpinning piers will extend beneath the neighboring properties, which will require an
encroachment agreement with neighboring property owners. If it is not feasible to install the
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underpinning piers beneath the adjacent property, the basement wall should be offset from the
property line by at least 18 inches to provide space for the shoring and the shoring should be
designed to resist surcharge loads from neighboring foundations in addition to at-rest soil
pressures.
6.5 Temporary Cut Slope and Shoring
Excavations that will be deeper than five feet and will be entered by workers should be sloped or
shored in accordance with CAL-OSHA standards (29 CFR Part 1926). The shoring engineer
should be responsible for shoring design. The contractor should be responsible for the
construction and safety of temporary slopes.
We anticipate an excavation extending up to about 12 feet bgs will be needed to construct the
below-grade parking garage and foundations. If parking lifts will be installed in the basement
level, we anticipate the excavation may extend up to a depth of about 18 feet bgs. We judge that
temporary cuts in clay which are less than 12 feet high, above groundwater, and inclined no
steeper than 1:1 (horizontal:vertical) will be stable provided they are not surcharged by
equipment, building foundations, or building material. Temporary shoring will be required
where temporary slopes are not possible because of space constraints. There are several key
considerations in selecting a suitable shoring system. Those we consider of primary concern are:
protection of surrounding improvements, including roadways, utilities, and adjacent structures
proper construction of the shoring system to reduce potential for ground movement
cost.
Several methods of shoring are available; we have qualitatively evaluated the following systems:
conventional soldier pile and lagging with or without tie backs
soil nails.
We judge that a soldier pile and timber lagging shoring system would be the most appropriate
shoring type for this project. A soldier pile and lagging shoring system usually consists of steel
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H-beams and concrete placed in predrilled holes extending below the bottom of the excavation.
Wood lagging is placed between the piles as the excavation proceeds. Where the required cut is
less than about 14 feet, a soldier pile and lagging system can typically provide economical
shoring without tiebacks and, therefore, will not encroach beyond the property line. Where cuts
exceed about 14 feet in height, soldier pile-and-lagging systems are typically more economical if
they include tiebacks. However, if tiebacks will extend beneath the streets and sidewalks and
adjacent properties, an encroachment agreement will be required with the City of Berkeley and
adjacent property owners. In our experience tiebacks will not be allowed within the BART ZOI.
If permission from the adjacent property owners or City of Berkeley cannot be obtained to install
tiebacks beneath their properties, then internal bracing will be required. It will be necessary to
provide between 12 and 18 inches of space between the property line and the face of the shoring
where the basement walls will be constructed adjacent to private property.
A soil-nail shoring system is an alternative soldier pile and lagging. Soil-nail shoring system
consists of reinforcing bars, which are grouted in predrilled holes through the face of the
excavation, and a reinforced shotcrete facing. Soil-nail shoring systems require a certain amount
of ground movement to mobilize their lateral resistance; for soil-nail shoring systems located
adjacent to existing structures, the soil-nail shoring system should be designed to limit lateral
movement to 1/2 inch. Furthermore, installation of soil-nail shoring systems requires temporary
vertical cuts on the face of excavation, about four feet in height, until each section of soil-nails
are installed and shotcrete facing is constructed. Therefore, soil-nail shoring systems are
appropriate for excavations in stiff clay where temporary vertical cuts are achievable. The
results of our Borings B-1, B-2, B-3, and B-5 indicate the subsurface soil in the upper 12 feet is
primarily sandy clay with gravel along the western and southern property line; at Boring B-4,
located at the northeastern portion of the site, the upper 9 feet of soil consists of medium dense
clayey sand that is not appropriate for installation of soil nails.
The safety of workers and equipment in or near the excavation is the responsibility of the
contractor. The selection, design, construction, and performance of the shoring system should be
the responsibility of the contractor. A structural engineer knowledgeable in this type of
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construction should design the shoring. Recommendations for the design and construction of a
soil-nail and soldier pile and lagging shoring systems are presented in Section 7.7.
Neighboring buildings are present in some locations outside the proposed excavation. Where the
foundations of neighboring buildings are within the zone of influence of the excavation, defined
by a 1.5:1 (horizontal:vertical) plane extending up from the bottom of excavation, the shoring
system should to be designed to limit lateral movement to less than 1/2 inch. A monitoring
program should be implemented during construction to monitor vertical and lateral movement of
improvements surrounding the site.
6.6 Excavation Dewatering
We anticipate excavations for the basement garage, parking lift pits, and foundations may extend
below the design groundwater level. The actual groundwater level at the time of construction is
uncertain. If construction is performed during the wet season, the water level may be close to the
design groundwater level and some level of dewatering will likely be required. We anticipate
dewatering can be performed, where necessary, using a passive system consisting of trench
drains and sump pumps. The need for, selection, and design of a dewatering system for the
project is the responsibility of the contractor.
6.7 Excavation, Monitoring, and Construction Considerations
The soil to be excavated for the proposed foundations and utilities is expected to consist
primarily of sandy clay with gravel which can be excavated with conventional earth-moving
equipment such as backhoes.
There are existing buildings adjacent to the site. Heavy equipment should not be used within
10 horizontal feet from adjacent buildings. Jumping jack or hand-operated vibratory plate
compactors should be used for compacting fill within this zone.
During excavation, the shoring system may deform laterally, which could cause the ground
surface adjacent to the shoring to settle. The magnitudes of shoring movements and the resulting
settlements are difficult to estimate because they depend on many factors, including the method
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of installation and the contractor's skill in the shoring installation. Ground movements due to a
properly designed and constructed shoring system should be within ordinary accepted limits of
about one inch where there are no improvements within a horizontal distance equal to 1.5 times
the height of the shoring and 1/2 inch where there are improvements within that horizontal
distance. A monitoring program should be established to evaluate the effects of the excavation
on the adjacent buildings and surrounding ground.
The contractor should establish survey points on the shoring and on adjacent buildings and
streets within 25 feet of the excavation perimeter prior to the start of excavation. Temporary
shoring located within the BART ZOI should also be monitored per BART requirements. The
survey points should be used to monitor the vertical and horizontal movements of the shoring
and surrounding structures and streets during construction. The contractor should also survey
and take photographs of existing buildings within a horizontal distance of 25 feet of the proposed
excavation limits prior to the start of construction.
6.8 Soil Corrosivity
Laboratory testing was performed by Sunland Analytical of Rancho Cordova, California on two
samples of soil obtained during our field investigation from Borings B-4 at a depth of 2 feet bgs
and B-5 at a depth of 5-1/2 feet bgs. The results of the test are presented in Appendix B of this
report.
Based on the results of the pH test for B-5, which indicate the near-surface soil has a pH of 6.0,
we conclude the soil at this site is “moderately corrosive” to buried metal. Furthermore, the
resistivity test results indicate the sample is “moderately corrosive.” Accordingly, all buried
iron, steel, cast iron, ductile iron, galvanized steel and dielectric-coated steel or iron may need to
be protected against corrosion depending upon the critical nature of the structure. If it is
necessary to have metal in contact with soil, a corrosion engineer should be consulted to provide
recommendations for corrosion protection. The results indicate that sulfate ion concentrations
are sufficiently low such that they do not to pose a threat to buried concrete. In addition, the
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chloride ion concentrations are insufficient to impact steel reinforcement in concrete structures
below ground adversely.
7.0 RECOMMENDATIONS
Recommendations regarding site grading, temporary shoring, foundation support, basement wall
design, and other geotechnical aspects of the project are presented in this section.
7.1 Site Preparation and Grading
Site demolition should include the removal of existing pavements and all existing underground
utilities. Demolished asphalt concrete should be taken to an asphalt recycling facility.
Demolished concrete and aggregate base beneath existing pavements may be re-used as select
fill if carefully segregated. Any vegetation and the upper 3 to 4 inches of organic topsoil should
be stripped in areas to receive improvements (i.e., building, pavement, or flatwork).
In general, abandoned underground utilities should be removed to the property line or service
connections and properly capped or plugged with concrete. Where existing utility lines are
outside of the proposed building footprint and will not interfere with the proposed construction,
they may be abandoned in place provided the lines are filled with lean concrete or cement grout
to the property line. Any excavations created during demolition should be properly backfilled
with compacted fill under the observation of our field engineer.
During demolition of the existing site improvements, care should be taken by the contractor to
ensure that excessive vibrations of the ground close to the adjacent structures do not occur. Any
piece of pneumatic machinery used in the demolition process should be restricted to working at
the center of the site, away from the adjacent buildings.
7.1.1 Soil Subgrade Preparation
We anticipate the soil subgrade for the basement slab/mat will consist of firm native soil with
near optimum moisture content. Therefore, scarifying, moisture conditioning and recompacting
the soil subgrade for the basement slab/mat will not be required. The basement slab/mat
subgrade should be proof-rolled prior to being covered up with mud slab or improvements.
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Excavation for the building pad subgrade will likely expose native moderately expansive clay.
The subgrade will be near or below the design groundwater level, and the exposed material may
be wet and sensitive to disturbance from equipment. Care should be taken to minimize
disturbance to the building pad subgrade during excavation. Heavy rubber-tired equipment
should not be driven on the subgrade to reduce the potential for subgrade “pumping.” We
recommend only tracked equipment be used when the excavation approaches two feet of the
subgrade elevation. Even with lightweight tracked equipment, soft subgrade areas may be
encountered. If soft areas are encountered in the building pad subgrade, subgrade stabilization
measures may be required. Recommendations for soil subgrade stabilization are presented in
Section 7.1.2.
7.1.2 Soil Subgrade Stabilization
In some areas, soft, wet soil may be exposed during excavation causing the subgrade to deflect
and rut under the weight of grading equipment. In these areas, some form of subgrade
stabilization may be required. Several options for stabilizing subgrade exist, as presented below.
Aeration
Aeration consists of mixing and turning the soil to lower the moisture content to an acceptable
level. Aeration typically requires several days to a week of warm, dry weather to effectively dry
the material. Material to be dried by aeration should be scarified to a depth of at least 12 inches;
the scarified material should be turned at least twice a day to promote uniform drying. Once the
moisture content of the aerated soil has been reduced to acceptable levels, the soil should be
compacted in accordance with our previous recommendations. Aeration is typically the least
costly subgrade stabilization alternative; however, it generally requires the most time to complete
and may not be effective in locations where the excavation is near the groundwater table.
Overexcavation
Another method of achieving suitable subgrade in areas where soft, wet soil is exposed is to
overexcavate the soft subgrade soil and replace it with drier, granular material. If the soft
material extends to great depths, the upper 18 to 24 inches of soft material may be overexcavated
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and a geotextile tensile fabric (Mirafi 500X or equivalent) placed beneath the granular backfill to
help span over the weaker material. The fabric should be pulled tight and placed at the base of
the overexcavation, extending at least two feet laterally beyond the limits of the overexcavation
in all directions. The fabric should be overlapped by at least two feet at all seams. Granular
material such as Class 2 aggregate base (AB) should then be placed and compacted over the
geotextile tensile fabric. Where the overexcavation extends below the groundwater, the granular
backfill should consist of drain rock. Drain rock should be overlain by geotextile filter or tensile
fabric (Mirafi 140NC or equivalent) to form a separation between the open-graded rock and soil
backfill placed above the rock.
Where very soft subgrade conditions are encountered, a geogrid, such as Tensar TriAx TX140 or
equivalent, may be required in lieu of tensile fabric. Where geogrids are used the depth of
overexcavation will likely be on the order of 12 to 18 inches. The geogrids should be overlapped
by at least two feet and tied with hog rings or nylon ties at a spacing not to exceed 10 feet. The
geogrids should be covered with a well-graded granular fill such as Class 2 AB; open-graded
rock should not be used. All backfill placed over the geogrid should be compacted in accordance
with our previous recommendations.
Chemical Treatment
Lime and/or cement have been successfully used to dry and stabilize fine-grained soils with
varying degrees of success. Lime- and/or cement-treatment will generally decrease soil density,
change its plasticity properties, and increase its strength. The degree to which lime will react
with soil depends on such variables as type of soil, mineralogy, quantity of lime, and length of
time the lime-soil mixture is cured. Cement is generally used in when a significant amount of
granular material or low-plasticity silt is present in the soil. The quantity of lime and/or cement
added generally ranges from 3 to 7 percent by weight and should be determined by laboratory
testing. The specialty contractor performing the chemical treatment should select the most
appropriate additive and quantity for the soil conditions encountered.
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If chemical treatment is used to stabilize soft subgrade, a treatment depth of about 18 inches
below the final soil subgrade will likely be required. The soil being treated should be scarified
and thoroughly broken up to full depth and width. The treated soil should not contain rocks or
soil clods larger than three inches in greatest dimension. Treated soil should be compacted to at
least 90 percent relative compaction8 (RC), and at least 95 percent RC in the upper six inches of
pavement subgrade.
7.1.3 Fill Materials and Compaction Criteria
On-site soil may be used as fill or backfill, provided it is free of organic matter, contains no rocks
or lumps larger than three inches in greatest dimension, and is approved by the Geotechnical
Engineer. Fill consisting of imported soil (select fill) should be free of organic matter, contain
no rocks or lumps larger than three inches in greatest dimension, have a liquid limit of less than
40 and a plasticity index lower than 12, and be approved by the Geotechnical Engineer. Samples
of proposed imported fill material should be submitted to the Geotechnical Engineer at least
three business days prior to use at the site. The grading contractor should provide analytical test
results or other suitable environmental documentation indicating the imported fill is free of
hazardous materials at least three days before use at the site. If this data is not available, up to
two weeks should be allowed to perform analytical testing on the proposed imported material.
Fill should be placed in horizontal lifts not exceeding eight inches in uncompacted thickness,
moisture-conditioned to above optimum moisture content, and compacted to at least 90 percent
RC. Fill material consisting of clean sand or gravel (defined as soil with less than 10 percent
fines by weight) should be compacted to at least 95 percent RC. Fill greater than five feet in
thickness or fill placed within the upper eight inches of vehicular pavement soil subgrade should
also be compacted to at least 95 percent RC, and be non-yielding.
8 Relative compaction refers to the in-place dry density of soil expressed as a percentage of the
maximum dry density of the same material, as determined by the ASTM D1557 laboratory compaction procedure.
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Where the recommended compaction requirements are in conflict with the City of Berkeley
standard details for pavements, sidewalks, or trenches within the public right-of-way, the City
Engineer or inspector should determine which compaction requirements should take precedence.
Controlled Low Strength Material
Controlled low strength material (CLSM) may be considered as an alternative to fill beneath the
building, concrete flatwork, or pavement. CLSM should meet the requirements in the
2015 Caltrans Standard Specifications. It is an ideal backfill material when adequate room is
limited or not available for conventional compaction equipment, or when settlement of the
backfill must be minimized. No compaction is required to place CLSM. CLSM should have a
minimum 28-day unconfined strength of 50 pounds per square inch (psi).
7.1.4 Utility Trench Backfill
Excavations for utility trenches can be readily made with a backhoe. All trenches should
conform to the current CAL-OSHA requirements. To provide uniform support, pipes or conduits
should be bedded on a minimum of four inches of sand or fine gravel. After the pipes and
conduits are tested, inspected (if required) and approved, they should be covered to a depth of
six inches with sand or fine gravel, which should be mechanically tamped.
Backfill for utility trenches and other excavations is also considered fill, and should be placed
and compacted as according to the recommendations previously presented. If imported clean
sand or gravel (defined as soil with less than 10 percent fines) is used as backfill, it should be
compacted to at least 95 percent relative compaction. Jetting of trench backfill should not be
permitted. Special care should be taken when backfilling utility trenches in pavement areas.
Poor compaction may cause excessive settlements, resulting in damage to the improvements
above the fill.
Foundations for the proposed structures should be bottomed below an imaginary line extending
up at a 1.5:1 (horizontal to vertical) inclination from the base of the utility trenches running
parallel to the foundation. Alternatively, the portion of the utility trench (excluding bedding) that
is below the 1.5:1 line can be backfilled with CLSM. If utility trenches are to be excavated
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below this zone-of-influence line after the construction of the building foundations, the trench
walls need to be fully supported with shoring until CLSM is placed.
7.1.5 Exterior Flatwork Subgrade Preparation
We recommend a minimum of four inches of Class 2 AB be placed below exterior concrete
flatwork, including patio slabs and sidewalks; the AB should extend at least six inches beyond
the slab edges where adjacent to landscaping. Class 2 AB beneath exterior slabs-on-grade, such
as patios and sidewalks, should be compacted in accordance with the requirements provided
above in Section 7.1.3.
7.2 Foundations
Our recommendations for spread footing and mat foundations are presented in this section.
7.2.1 Spread Footings
The proposed building may be supported on conventional spread footings bearing on firm native
soil. Continuous footings should be at least 18 inches wide and isolated spread footings should
be at least 24 inches wide. Footings should be bottomed at least 18 inches below the lowest
adjacent soil subgrade.
The footings may be designed using allowable bearing pressures of 5,000 pounds per square foot
(psf) for dead-plus-live loads; this value may be increased by one-third for total design loads,
which include wind or seismic forces. These allowable bearing capacities include factors of
safety of at least 2.0 and 1.5 for dead-plus-live loads and total loads, respectively.
Lateral loads can be resisted by a combination of passive pressure on the vertical faces of the mat
and friction along the bottom of the mat. Lateral resistance may be computed using an allowable
passive pressure of 2,000 psf (uniform distribution) for transient loads, including wind and
seismic, and equivalent fluid weights (triangular distribution) of 260 and 125 pounds per cubic
foot (pcf) for sustained loads above and below the design groundwater table, respectively.
Passive resistance in the upper one foot of soil should be ignored unless it is confined by slabs or
pavement. To compute frictional resistance, we recommend using a friction coefficient of 0.3.
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The above-recommended passive pressure and frictional resistance values include a factor of
safety of at least 1.5 and may be used in combination without reduction.
Footing excavations should be free of standing water, debris, and disturbed materials prior to
placing concrete. If footings are excavated during the rainy season and/or whether the
excavations extend below the groundwater level at the time of construction, they should
incorporate a rat slab to protect the footing subgrade. This will involve over-excavating the
footing by about two inches and placing lean concrete or sand-cement slurry in the bottom
(following inspection by our engineer). A rat slab will help protect the footing subgrade during
placement of reinforcing steel. Water can then be pumped from the excavations prior to
placement of structural concrete, if present. The bottoms and sides of the footing excavations
should be moistened following excavation and maintained in a moist condition until concrete is
placed. We should check footing excavations prior to placement of reinforcing steel.
7.2.2 Mat Foundation
For structural design of the mat foundation, we recommend using an initial coefficient of vertical
subgrade reaction of 40 pounds per cubic inch (pci) under DL+LL conditions; this value may be
increased by 50 percent for total load conditions. The coefficient of vertical subgrade values
have been reduced to account for the size of the mat/equivalent footings (therefore, this is not kv1
for 1-foot-square plate). We recommend the mat be designed using an allowable bearing
pressure of 5,000 pounds per square foot (psf) for dead-plus-live loads; we anticipate the average
bearing pressure will be significantly lower. This value may be increased by one-third for total
loads (including seismic and wind loads).
Lateral loads can be resisted by a combination of passive pressure on the vertical faces of the mat
and friction along the bottom of the mat. Lateral resistance may be computed using an allowable
passive pressure of 2,000 psf (uniform distribution) for transient loads, including wind and
seismic, and equivalent fluid weights (triangular distribution) of 260 and 125 pcf for sustained
loads above and below the groundwater table, respectively. Passive resistance in the upper one
foot of soil should be ignored unless it is confined by slabs or pavement. To compute frictional
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resistance, we recommend using a friction coefficient of 0.3 where the mat is in contact with the
soil. Where a vapor retarder is placed beneath the mat, a base friction coefficient of 0.20 should
be used. Where the mat is underlain by waterproofing membrane, the allowable friction factor
will depend on the type of waterproofing used at the base of the mat. For bentonite-based
waterproofing membranes, such as Paraseal or Voltex, a friction factor of 0.12 should be used
(assumes a bentonite friction angle of 10 degrees). If Preprufe is used, a base friction factor of
0.20 should be used. Friction factors for other types of waterproofing membranes can be
provided upon request. The above-recommended passive pressure and frictional resistance
values include a factor of safety of at least 1.5 and may be used in combination without
reduction.
The subgrade should be kept moist and be free of standing water, debris, and disturbed materials
and be checked by the project Geotechnical Engineer prior to being covered up by the underslab
drainage system or waterproofing. Where waterproofing will be installed, we recommend a rat
slab consisting of at least three inches of structural concrete or CLSM be placed on the mat
subgrade to protect the subgrade from softening from ponding water and/or disturbance from
foot traffic during construction, and to provide a working surface on which to install the
waterproofing system.
7.3 Underslab Drainage System
Where the garage floor slab will extend below the design groundwater level, an underslab
drainage system should be installed to reduce hydrostatic pressures. Alternatively, the floor
slab/mat can be waterproofed and the foundations and floor slab be designed to resist hydrostatic
pressures.
Based on our experience, we believe a permanent underslab drainage system to reduce
hydrostatic pressures may result in a more economical foundation design than a fully
waterproofed basement designed to resist hydrostatic pressures. We recommend the permanent
underslab drainage system consist of a series of 12-inch-wide trenches that are at least 12 inches
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deep and sloped to drain at an inclination of at least one percent to a sump. The trenches should
be spaced no more than 20 feet on center.
The garage slab subgrade (between the trenches) should be excavated to provide room for at
least six inches of Class 2 permeable material and should be sloped at an inclination of at least
two percent toward the subdrain trenches. The Class 2 permeable material should meet the
requirements of Caltrans Standard Specifications 68-1.025 most recent edition. The collection
pipes should consist of four-inch-diameter, Schedule 40, perforated PVC pipe (perforations
down). The pipes should be installed such that they are surrounded on all sides by at least four
inches of permeable material and a filter sock should be installed around the pipe to prevent the
finer particles of the Class 2 permeable material from entering the perforations.
The pipes should drain at a gradient of at least one percent to at least one sump pit location in the
garage level. Cleanouts should be provided to ensure the underslab drainage system can be
cleared if it becomes clogged. The sump-and-pump system should be designed to discharge
water directly to the storm drain system without allowing the water to build up beneath the slab-
on-grade floor. It is critical that the sump pump(s) remain functioning during periods of elevated
groundwater; therefore, back-up generators should be considered in the design of the sump-and-
pump system, if used. In the event that water is allowed to build up beneath the slab, structural
damage and flooding of the garage space may occur. Therefore, we recommend that “pop-off”
valves be installed in the floor slab to allow excess water to drain into the garage in case of
hydrostatic pressure build up beneath the floor slab.
7.4 Slab-on-Grade Floor
Where the garage floor slab will extend below the design groundwater level, an underslab
drainage system should be installed to reduce hydrostatic pressures or the slab be waterproofed
and designed to resist the hydrostatic uplift pressure. If an underslab drainage system will be
installed, the design of the underslab drainage system should consider the possibility that a
portion of the drainage system may fail, resulting in a build-up of hydrostatic pressures which
could damage the floor slab. Therefore, we recommend that “pop-off” valves be installed in the
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floor slab to allow excess water to drain into the garage in case of hydrostatic pressure build up
beneath the floor slab.
Where water vapor transmission through the floor slab is undesirable and waterproofing is not
installed below the floor slab, we recommend installing a water vapor retarder beneath the floor.
A vapor retarder is generally not required beneath parking garage floor slabs because there is
sufficient air circulation to allow evaporation of moisture that is transmitted through the slab;
however, we recommend the vapor retarder be installed below the slab-on-grade in utility rooms
and any areas in or adjacent to the parking garage that will be used for storage and/or will receive
a floor covering or coating.
The vapor retarder may be placed directly on the Class 2 permeable material. The vapor retarder
should meet the requirements for Class A vapor retarders stated in ASTM E1745. The vapor
retarder should be placed in accordance with the requirements of ASTM E1643. These
requirements include overlapping seams by six inches, taping seams, and sealing penetrations in
the vapor retarder.
If required by the structural engineer, the vapor retarder may be covered with two inches of sand
to aid in curing the concrete and to protect the vapor retarder during slab construction. The sand
overlying the vapor retarder should be moist at the time concrete is placed. However, excess
water trapped in the sand could eventually be transmitted as vapor through the slab. Therefore, if
rain is forecast prior to pouring the slab, the sand should be covered with plastic sheeting to
avoid wetting. If the sand becomes wet, concrete should not be placed until the sand has been
dried or replaced.
Concrete mixes with high water/cement (w/c) ratios result in excess water in the concrete, which
increases the cure time and results in excessive vapor transmission through the slab. Therefore,
concrete for the floor slab should have a low w/c ratio - less than 0.50. If approved by the
project structural engineer, the sand can be eliminated and the concrete can be placed directly
over the vapor retarder, provided the w/c ratio of the concrete does not exceed 0.45 and water is
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not added in the field. If necessary, workability should be increased by adding plasticizers. In
addition, the slab should be properly cured.
Before the floor covering is placed, the contractor should check that the concrete surface and the
moisture emission levels (if emission testing is required) meet the manufacturer’s requirements.
7.5 Permanent Below-Grade Walls
Below-grade walls should be designed to resist static lateral earth pressures, lateral pressures
caused by earthquakes, vehicular surcharge pressures, and surcharges from adjacent foundations,
where appropriate. We recommend restrained below-grade walls at the site be designed for the
more critical of the following criteria:
At-rest equivalent fluid weight of 55 pcf above the design groundwater table and 90 pcf below, plus a traffic increment where the wall will be within 10 feet of adjacent streets.
Active pressure of 40 pcf plus a seismic increment of 36 pcf (triangular distribution) above the design groundwater level, and 80 pcf below the groundwater level plus a seismic increment of 17 pcf (triangular distribution).
Where an underslab drainage system is installed and the basement wall is properly backdrained,
the entire height of basement wall may be designed using the recommended at-rest and active
plus seismic increment values for above the design groundwater level; we should address this
condition when the final depth of basement wall and dewatering system are available.
The recommended pressures above are based on a level backfill condition with no additional
surcharge loads. Where the permanent wall will be subject to vehicular loading within 10 feet of
the wall, an additional uniform lateral pressure of 50 psf applied to the upper 10 feet of the wall.
If neighboring building foundations are not underpinned and rest on soil above an imaginary line
that lies at an inclination of 1.5:1 (horizontal to vertical) projected upward from the bottom edge
of the basement wall, the basement wall should be designed for surcharge pressures from the
neighboring building foundations.
The lateral earth pressures recommended are applicable to walls that are backdrained to prevent
the buildup of hydrostatic pressure. One acceptable method for back-draining a basement wall is
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to place a prefabricated drainage panel against the back of the wall. The drainage panel should
extend down to the design groundwater table or to a perforated PVC collector pipe where the
wall bottoms above the design groundwater table. The pipe should be surrounded on all sides by
at least four inches of Caltrans Class 2 permeable material or 3/4-inch drain rock wrapped in
filter fabric (Mirafi NC or equivalent). A proprietary, prefabricated collector drain system, such
as Tremdrain Total Drain or Hydroduct Coil (or equivalent), designed to work in conjunction
with the drainage panel may be used in lieu of the perforated pipe surrounded by gravel
described above. The pipe should be connected to a suitable discharge point; a sump and pump
system may be required to drain the collector pipes, in the event the elevation is insufficient to
gravity drain to the storm drain system.
To protect against moisture migration, below-grade basement walls should be waterproofed and
water stops should be placed at all construction joints. In recent years, we have observed
numerous leaks in below-grade portions of buildings constructed with waterproofed, shotcrete
walls. In areas where there is a high sensitivity to leaks, we recommend cast-in-place concrete
be considered.
If backfill is required behind below-grade walls, the walls should be braced, or hand compaction
equipment used, to prevent unacceptable surcharges on walls (as determined by the structural
engineer).
7.6 Underpinning
Where hand-excavated underpinning piers are used to underpin adjacent foundations, the piers
should be designed to gain support through end bearing on firm native soil. An allowable
bearing pressure of 5,000 psf for dead-plus-live loads may be used for designing of underpinning
piers. The underpinning piers should extend at least 24 inches below the planned excavations for
the project or 24 inches above an imaginary line that lies at an inclination of 1.5:1 (horizontal to
vertical) projected upward from the bottom edge of the excavation. The width of the
underpinning piers should be determined by the project Structural Engineer or underpinning
designer based on the ability of the existing foundation to span an area of non-support. If fill or
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weak soil is encountered at the bottom of the underpinning piers, the excavation should be
deepened until suitable bearing firm native soil is encountered as directed by the project
Geotechnical Engineer in the field. Underpinning should be designed for unbalanced horizontal
loads resulting from the soil retained by the piers computed using an at-rest equivalent fluid
weight of 55 pcf above the design groundwater table and an at-rest equivalent fluid weight of
90 pcf below the design groundwater table, plus surcharge from adjacent foundations bearing
above an imaginary 1.5:1 (horizontal to vertical) line projected up from the bottom edge of the
excavation. Lateral resistance for underpinning piers may be computed using the passive
pressure and friction factor values for spread footings presented in Section 7.2.1 above.
7.7 Temporary Cut Slopes and Shoring
We anticipate excavations of about 12 and 18 feet bgs below existing grade will be needed to
construct the proposed one-level basement parking garage and parking lifts, respectively. The
soil to be excavated would consist of predominately clay, sand and gravel, which can be
excavated using conventional earth-moving equipment such as loaders and backhoes. We judge
that temporary slope cuts in clayey soils, corresponding to CAL-OSHA Types B soil, above the
groundwater table inclined no steeper than 1:1 (horizontal:vertical), will be stable provided that
they are not surcharged by equipment, adjacent building foundations, or building material.
Temporary shoring will be required where temporary slopes are not possible because of space
constraints. The shoring engineer should be responsible for shoring design. The contractor
should be responsible for the construction and safety of temporary slopes. We should review the
geotechnical aspects of the proposed shoring system to ensure that it meets our requirements.
During construction, we should observe the installation of the shoring system and check the
condition of the soil encountered during excavation.
As discussed in Section 6.5, we conclude soil-nail and soldier pile and lagging shoring systems
are appropriate for support of excavations for this project. Recommendations for soil-nail and
soldier pile and lagging temporary shoring systems are presented in this section.
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7.7.1 Cantilevered Soldier Pile and Lagging Shoring
We recommend the cantilevered soldier pile-and-lagging shoring system be designed to resist an
active equivalent fluid weight of 40 pcf where the retained ground surface is level. In locations
where minimizing lateral deflections is critical, such as near adjacent buildings, near sensitive
underground utilities or within the BART ZOI, the shoring system should be designed to resist
an at-rest equivalent fluid weight of 55 pcf (level ground surface) plus any foundation surcharge
loads. Where traffic loads are expected within 10 feet of the shoring walls, an additional design
load of 50 psf should be applied to the upper 10 feet of the wall. Where construction equipment
will be working behind the walls within a horizontal distance equal to the wall height, the design
should include a surcharge pressure of 250 psf.
The above pressures should be assumed to act over the entire width of the lagging installed
above the excavation. The above pressures assume that during construction, groundwater, if
encountered, will seep through the lagging and will not build-up behind the soldier pile and
lagging temporary shoring system. Where appropriate, the shoring system should be designed to
resist the surcharge pressures imposed by adjacent structures. The surcharge pressures should be
evaluated when the foundation type, load, and elevation are known.
Passive resistance at the toe of the soldier pile should be computed using equivalent fluid
weights of 260 and 125 pcf above and below the groundwater table at the time of construction,
respectively; however, the passive pressure should be limited to 2,000 psf with depth. Passive
pressure can be assumed to act over an area of three soldier pile widths assuming the toe of the
soldier pile is filled with structural concrete. The shoring designer should check that the
specified minimum concrete strength is sufficient to spread the anticipated loads to three soldier
pile widths. If the soldier piles are vibrated into place, rather than being placed into drilled holes
with concrete, then the passive pressure should only be applied to three beam flange widths.
These passive pressure values include a factor of safety of at least 1.5.
Soldier piles should be placed in pre-drilled holes backfilled with concrete or installed in soil-
mix columns. The subsurface soils include lenses of clayey sands. Therefore, the shoring
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contractor should be prepared to use casing or drilling slurry to reduce caving of holes, where
necessary. Installing soldier piles using a vibratory method is not recommended within 25 feet
of existing structures.
The penetration of the soldier piles must be sufficient to ensure stability and resist the downward
loading of tiebacks. Vertical loads can be resisted by skin friction along the portion of the
soldier piles below the excavation. We recommend using an allowable skin friction value of
1,000 psf to compute the required soldier pile embedment. End bearing should be neglected.
7.7.2 Soldier Pile and Lagging Shoring System with Tiebacks
Recommended lateral pressures for the design of soldier pile and lagging shoring with tiebacks
are presented on Figure 7. Where it is not feasible to install tiebacks, then internal bracing of the
excavation will be required. Internal bracing should be preloaded to limit movement of the
shoring. In calculating these design pressures, we assumed drained conditions with no
hydrostatic pressure acting on the shoring. Where traffic loads are expected within 10 feet of the
shoring walls, an additional design load of 50 psf should be applied to the upper 10 feet of the
wall. Where construction equipment will be working behind the walls within a horizontal
distance of 10 feet, the design should include a surcharge pressure of 250 psf acting over the
upper 10 feet of the wall. The above pressures should be assumed to act over the entire width of
the lagging installed above the excavation. The shoring should be designed to resist the
surcharge pressures imposed by adjacent structures if the adjacent buildings are not underpinned.
The surcharge pressures should be evaluated when the foundation type, load, and elevation are
known.
Passive resistance at the toe of the soldier pile should be computed using equivalent fluid
weights of 260 and 125 pcf above and below the groundwater table, respectively, at the time of
construction; however, the passive pressure should be limited to 2,000 psf with depth. These
passive pressure values include a factor of safety of at least 1.5. The upper foot of soil should be
ignored when computing passive resistance. Passive pressure can be assumed to act over an area
of three soldier pile widths, or pile-to-pile spacing, whichever is less, assuming the toe of the
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soldier pile is filled with concrete or lean concrete that is sufficiently strong to accommodate the
corresponding stresses.
Soldier piles should be placed in pre-drilled holes backfilled with concrete or installed in soil-
mix columns. There are interbedded lenses of sands and gravels, therefore, the shoring
contractor should be prepared to use casing or drilling slurry to reduce caving of holes, where
necessary. Installing soldier piles using a vibratory method is not recommended within 25 feet
of existing structures.
The penetration of the soldier piles must be sufficient to ensure stability and resist the downward
loading of tiebacks. Vertical loads can be resisted by skin friction along the portion of the
soldier piles below the excavation. We recommend using an allowable skin friction value of
1,000 psf to compute the required soldier pile embedment. End bearing should be neglected.
Design criteria for tiebacks are also presented on Figure 7. As shown, tiebacks should derive
their load-bearing capacity from the soil behind an imaginary line sloping upward from a point
H/5 feet away from the bottom of the excavation at an angle of 60 degrees from horizontal,
where H is the wall height in feet. The minimum stressing lengths for strand and bar tendons
should be 15 and 10 feet, respectively. The minimum bond length for strand and bar tendons
should both be 15 feet.
Allowable capacities of the tiebacks will depend upon the drilling method, hole diameter, grout
pressure, and workmanship. The shoring contractor should use a smooth-cased method (such as
a Klemm rig) to install the tiebacks beneath adjacent buildings, where applicable. The shoring
designer should be responsible for determining the actual length of tiebacks required to resist the
design loads. The determination should be based on the designer’s familiarity with the
installation method to be used.
Tieback Testing
The computed bond length of tiebacks should be confirmed by a performance- and proof-testing
program under the observation of our field engineer. The first two production tiebacks and two
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percent of the remaining tiebacks should be performance tested to 1.5 times the design load. The
remaining tiebacks should be confirmed by a proof-test to 1.25 times the design load. The
movement of each tieback should be monitored with a free-standing, tripod-mounted dial gauge
during performance and proof testing. The bottom of excavation should not extend more than
two feet below a row of unsecured tiebacks.
The performance test is used to verify the capacity and the load-deformation behavior of the
tiebacks. It is also used to separate and identify the causes of tieback movement, and to check
that the designed unbonded length has been established. In the performance test, the load is
applied to the tieback in several cycles of incremental loading and unloading. During the test,
the tieback load and movement are measured. The maximum test load should be held for a
minimum of 10 minutes, with readings taken at 0, 1, 3, 6, and 10 minutes. If the difference
between the 1- and 10-minute reading is less than 0.04 inch during the loading, the test is
discontinued. If the difference is more than 0.04 inch, the holding period is extended by 50
minutes to 60 minutes, and the movements should be recorded at 15, 20, 25, 30, 45, and 60
minutes.
A proof test is a simple test used to measure the total movement of the tieback during one cycle
of incremental loading. The maximum test load should be held for a minimum of 10 minutes,
with readings taken at 0, 1, 2, 3, 6, and 10 minutes. If the difference between the 1- and 10-
minute reading is less than 0.04 inch, the test is discontinued. If the difference is more than 0.04
inch, the holding period is extended by 50 minutes to 60 minutes, and the movements should be
recorded at 15, 20, 25, 30, 45, and 60 minutes.
We should evaluate the tieback test results and determine whether the tiebacks are acceptable. A
performance- or proof-tested tieback with a 10-minute hold is acceptable if the tieback carries
the maximum test load with less than 0.04 inch movement between 1 and 10 minutes, and total
movement at the maximum test load exceeds 80 percent of the theoretical elastic elongation of
the unbonded length.
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A performance- or proof-tested tieback with a 60-minute hold is acceptable if the tieback carries
the maximum test load with less than 0.08 inch movement between 6 and 60 minutes, and total
movement at the maximum test load exceeds 80 percent of the theoretical elastic elongation of
the unbonded length. Tiebacks that failed to meet the first criterion will be assigned a reduced
capacity.
7.7.3 Soil-Nail Shoring System
All or portions of the proposed excavation along the western and southern property lines may be
supported by a soil nail shoring system. Soil nail walls should be designed to resist static lateral
earth pressures, as well as traffic loads, construction equipment loads, and foundation surcharge
loads, where applicable. In general, we recommend the walls be designed and constructed in
accordance with the guidelines presented in the Federal Highway Administration report on soil
nail walls (FHWA, 2015)9. Several computer programs, such as SNAIL (California Department
of Transportation, 2014) and GoldNail (Golder Associates, 1996), are available for designing a
soil-nail wall. SNAIL uses a force equilibrium method of analysis; the failure planes are
assumed bi-linear if they pass through the toe of the wall and tri-linear if they pass below the toe
of the wall. GoldNail uses a slope-stability model that satisfies overall limiting equilibrium of
free bodies defined by circular slip surfaces.
Soil-nail systems are typically installed under a design-build contract by specialty contractors;
therefore, we are not providing a specific design. However, we are providing estimated input
parameters for preliminary design. The actual capacities and lengths should be determined by
the design-build contractor with experience designing, building, and testing soil-nail walls in
similar soil conditions. We should review the design prior to installation. For preliminary
design, we recommend the input parameters presented in Table 2.
9 Federal Highway Administration (2003), Geotechnical Engineering Circular No. 7 – Soil Nail Walls,
March 2003 (FHWA Report No. FHWA0-IF-03-017)
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TABLE 2 Recommended Input Parameters for Design of Soil-Nail Walls
Soil Type1 Total
Density (pcf)
Ultimate Bond Strength (psf)
(Factor of Safety = 1.0)
Shear Strength Parameters
c2 3
(psf) (deg)
Sandy Clay 120 1,000 2,000 0
Notes: 1 Assume upper 12 feet of soil consists of sandy clay. 2 Cohesion intercept or undrained shear strength, without a factor of safety 3 Angle of internal friction, without a factor of safety
The soil-nail wall should be backdrained using two-foot-wide prefabricated drainage panels
between the nails. The panels should extend to a drainage pipe at the base of the wall that directs
the water to a suitable outlet or to weep holes at the base of the wall. Where construction
equipment will be working or driving upslope within 10 feet of the soil-nail wall, the design
should include a surcharge pressure of 250 psf. Where appropriate, the shoring system should be
designed to resist the surcharge pressures imposed by adjacent structures. The surcharge
pressures should be evaluated when the foundation type, load, and elevation are known. The
soil-nail wall should be designed with a minimum factor of safety of 1.5 against slope stability
failure for temporary walls.
We should be allowed to review the design plans and design calculations prior to their issuance
for construction to check for conformance with our recommendations. The design of the walls
should also include appropriate testing of soil-nails.
Soil-Nail Testing
We recommend the soil-nails be load-tested prior to and during construction in accordance with
the guidelines presented in the FHWA document titled Soil Nail Walls Reference Manual, dated
February 2015 (Report No. FHWA-NHI-14-007). Test nails should be installed using the same
equipment, method, and hole diameter as planned for the production nails. Verification and
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proof tests should be performed. Verification tests are performed prior to production nail
installation to verify the pullout resistance (bond strength) value used in design. Two
verification tests should be performed for each soil type assumed in design. Proof tests are
performed during construction to verify that the contractor’s procedure remains the same or that
the nails are not installed in a soil type not tested during the verification stage testing. At least
five percent of the production nails should be proof tested.
Tests should be performed on production or sacrificial nails to a test load corresponding to the
ultimate pullout resistance value used in the design. Test nails should have at least one foot of
unbonded length and 10 feet of bond length. The nail bar grade and size should be designed
such that the bar stress does not exceed 80 percent of its ultimate strength during testing.
The verification and proof tests should be performed in accordance with FHWA guidelines
(FHWA, 2015), including the recommended load increments, maximum test load, and failure
criteria. We should evaluate the test results and determine whether the test nail performance is
acceptable.
7.8 Seismic Design
For design in accordance with the 2016 California Building Code, we recommend Site Class D
be used. Using the USGS U.S. Seismic Design Maps website and the site latitude of 37.8728º
and longitude of -122.2699º we conclude the following seismic design parameters should be
used:
SS = 2.354 g, S1 = 0.979 g
SMS = 2.354 g, SM1 = 1.468 g
SDS = 1.569 g, SD1 = 0.979 g
Seismic Design Category E for Risk Categories I, II, and III.
8.0 GEOTECHNICAL SERVICES DURING CONSTRUCTION
Prior to construction, Rockridge Geotechnical should review the project plans and specifications
to verify that they conform to the intent of our recommendations. During construction, our field
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engineer should provide on-site observation and testing during site preparation, placement and
compaction of fill, and installation of temporary shoring, underpinning piers and foundations.
These observations will allow us to compare actual with anticipated soil conditions and to verify
that the contractor's work conforms to the geotechnical aspects of the plans and specifications.
9.0 LIMITATIONS
This geotechnical study has been conducted in accordance with the standard of care commonly
used as state-of-practice in the profession. No other warranties are either expressed or implied.
The recommendations made in this report are based on the assumption that the subsurface
conditions do not deviate appreciably from those disclosed in the test borings. If any variations
or undesirable conditions are encountered during construction, we should be notified so that
additional recommendations can be made. The foundation recommendations presented in this
report are developed exclusively for the proposed development described in this report and are
not valid for other locations and construction in the project vicinity.
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REFERENCES
2016 California Building Code
2015 Caltrans Standard Specifications
A3GEO (2015). Geotechnical Investigation Report, Berkeley Way Project, University of California, Berkeley, June 17.
California Geological Survey (2003). State of California Seismic Hazard Zones, Oakland West Quadrangle, Official Map, February 14, 2003.
California Department of Transportation, Division of New Technology, Materials and Research, Office of Geotechnical Engineering, (2014). SNAIL Program, A User Manual, updated December 2014, available from http://www.dot.ca.gov/hq/esc/geotech/software/geo_software.html.
Cao, T., Bryant, W. A., Rowshandel, B., Branum D. and Wills, C. J. (2003). “The Revised 2002 California Probabilistic Seismic Hazard Maps”
Field, E.H., and 2014 Working Group on California Earthquake Probabilities, (2015). UCERF3: A new earthquake forecast for California’s complex fault system: U.S. Geological Survey 2015-3009, 6 p., http://dx.doi.org/10.3133/fs20153009.
Federal Highway Administration, (2015). Soil Nail Walls Reference Manual, Publication Number FHWA-NHI-14-007, February.
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Schultze & Associates, Inc. (2013). 1929 University Avenue, Berkeley, California, Report for: Installation of Two Monitoring Wells and First Quarterly Groundwater Monitoring Event, December 9.
Sitar, N. et al. (2012). Seismically Induced Lateral Earth Pressures on Retaining Structures and Basement Walls, ASCE GeoCongress 2012 Geotechnical Special Publiation No. 226.
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Subsurface Consultants, Inc. (1994). Final Report, Sumps and Hydraulic Hoists Removal, Soil and Groundwater Remediation, 2009, 2011, and 2015 Addison Street, Berkeley, California, October 21.
Toppozada, T.R. and Borchardt G. (1998). “Re-evaluation of the 1936 “Hayward Fault” and the 1838 San Andreas Fault Earthquakes.” Bulletin of Seismological Society of America, 88(1), 140-159.
U.S. Geological Survey (USGS) (2008). The Uniform California Earthquake Rupture Forecast, Version 2 (UCERF 2): prepared by the 2007 Working Group on California Earthquake Probabilities, U.S. Geological Survey Open File Report 2007-1437.
FIGURES
Project No. FigureDateROCKRIDGEGEOTECHNICAL 1
SITE LOCATION MAP
SITE
Base map: The Thomas Guide Alameda County 2002
0 1/2 Mile
Approximate scale
1/4
11/21/16 16-1193
2012 BERKELEY WAYBerkeley, California
0
Approximate scale
50 Feet
03/25/17 16-1193 2
Berkeley, California
SITE PLAN
Date Project No. Figure
ROCKRIDGEGEOTECHNICAL
Base map: Google Earth, 2016.
EXPLANATION
Approximate location of boring by RockridgeGeotechnical Inc., September 29 and 30, 2016
Approximate project limits
Approximate right-of-way of Bay Area RapidTransit (BART) limits
Location of generalized cross section showingzone-of-influence for BART Subway Structures,see Figure 3
BERKELEY WAY
HE
NR
Y S
TR
EE
T
B-1
B-2
B-1
B-5
B-4
B-3
UNIVERSITY AVENUE
SH
AT
TU
CK
A
VE
NU
E
Note: Location of BART right-of-way limitsestimated using the Record Map of Right ofWay, Berkeley-Richmond Line, Russell Streetto Grove Street, by Parsons Brinckerhoff TudorBectel Engineers, Package R-005, ContractK-501, Sheet RRW17, March 11, 1965
2012 BERKELEY WAY
A A'
A
A
'
SINGLE-STORYCOMMERCIAL
BUILDING
SINGLE-STORYCOMMERCIAL
BUILDING
SINGLE-STORYCOMMERCIAL
BUILDING
TWO-STORY
COMMERCIALBUILDING
THREE-STORYCOMMERCIAL
BUILDING
THREE-STORYCOMMERCIAL
BUILDING(NASH HOTEL)
TWO-STORYCOMMERCIAL
BUILDING
TWO-STORYRESIDENTIAL
BUILDING
TWO-STORYRESIDENTIAL
BUILDING
SINGLE-STORY STRUCTURE
TWO-STORYCOMMERCIAL
BUILDING
−−Depositional or intrusive contact, dashed where approximately located, dotted where concealed
−−Dashed where approximately located, small dashes where inferred, dotted where concealed, queried where location is uncertain.
−−Dotted where concealed
−−Shows fold axis, dotted where concealed
Contact - Depositional or intrusive contact, dashed where approximately located, dotted where concealed
Fault - Dashed where approximately located, small dashed where inferred, dotted where concealed, queried where locations is uncertainReverse or thrust fault - Dotted where concealed
Anticline -Shows fold axis, dotted where concealed
Syncline
Overturned bedding
Strike and dip of bedding
Flat beddingVertical beddingStrike and dip of foliationVertical foliation
Vertical jointStrike and dip of joints in plutonic rocks
0 4,000 Feet
Approximate scale
2,000
EXPLANATION af
Qhaf
Qhl
Qpaf
Tmb
KJfs
KJfm
Ku
Kfn
Kfgm
Jsv
sp
fg
Alluvial fan and fluvial deposits (Holocene)
Alluvial fan and fluvial deposits
Keratophyre and quartz keratophyre (Late Jurassic)
Sandstone of the Novato Quarry terrane ofBlake and others (1984) (Late Cretaceous)
Franciscan complex, melange (CretaceousLate Jurassic), includes mapped locally:
Chert blocks
Artificial fill (Historic)
Natural levee deposits (Holocene)
Morage Formation (late Miocene)
Franciscan complex, sandstone, undivided(Late Cretaceous to Late Jurassic)
Undivided Great Valley complex rocks(Cretaceous)
Fine-grained quartz deiorite (Late Cretaceous (?)
Greenstone blocks
Project No. FigureDate
SITE
4
REGIONAL GEOLOGIC MAP
Base map: USGS MF 2342, Geologic Map and Map Database of the Oakland Metropolitan Area, Alameda, Contra Costa, and San Francisco Counties, California (Graymer, 2000).
ROCKRIDGEGEOTECHNICAL 16-119311/21/16
2012 BERKELEY WAYBerkeley, California
Project No. FigureDate
Base Map: U.S. Geological Survey (USGS), National Seismic Hazards Maps - Fault Sources, 2008.
10 Miles
Approximate scale
0 5
5ROCKRIDGEGEOTECHNICAL
REGIONAL FAULT MAP
SITE
EXPLANATION
Strike slip
Thrust (Reverse)
Normal
16-119311/21/16
2012 BERKELEY WAYBerkeley, California
Point Reyes Fault
San Andreas FaultSan G
regorio Fault
Monte Vista-Shannon Fault
West N
apa
Mount Diablo Thrust
Greenville Fault
Great Valley 05
Great Valley 4b
Calaveras Fault
Green Valley
Hayward-Rodgers Creek Fault
Hayward-Rodgers Creek Fault
Project No. FigureDate 6
0 4,000 Feet
Approximate scale
2,000EXPLANATION
SITE
SEISMIC HAZARDS ZONE MAP
Earthquake-Induced Landslides; Areas where previous occurence of landslide movement, or local topographic, geological, geotechnical, and subsurface water conditions indicate a potential for permanent ground displacements.
Liquefaction; Areas where historic occurence of liquefaction, or local topographic, geological, geotechnical, and subsurfacewater conditions indicate a potential for permanent ground displacements.
Reference:State of California "Seismic Hazard Zones" Oakland West Quadrangle.Released on February 14, 2003
ROCKRIDGEGEOTECHNICAL 16-119311/21/16
2012 BERKELEY WAYBerkeley, California
APPENDIX A Logs of Borings
11213.950
S&H
S&H
S&H
S&H
S&H
S&H
S&H
CL
CL
CL
CL
CL
CL
CL
CL
CL
CL
3 inches of asphalt concrete9 inches of aggregate baseSANDY CLAY (CL)brown with light brown and red-brown, hard, moist,fine to medium sand
SANDY CLAY with GRAVEL (CL)brown with yellow and orange, hard, moist, finesand, angular fine gravelParticle Size Distribution; see Appendix B
SANDY CLAY (CL)brown, very stiff, moist
SANDY CLAY with GRAVEL (CL)brown mottled with red and yellow, very stiff, moist,subrounded fine gravel
CLAY (CL)brown with black staining, very stiff, moist, trace finesand
SANDY CLAY (CL)light brown, very stiff, moist, fine to medium sand
SANDY CLAY with GRAVEL (CL)brown, very stiff, moist, angular fine gravelSANDY CLAY (CL)light brown, very stiff, moist
CLAY with SAND (CL)brown mottled with olive and black staining, verystiff, moist, fine sand, trace coarse sand
SANDY CLAY (CL)brown mottled with olive and yellow, very stiff, moist,fine to coarse sand
32
45
22
22
27
22
17
141630
223034
131121
91219
71524
101319
7915
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
See Site Plan, Figure 2
9/29/16
Hollow-Stem
Logged by:
Hammer type: Downhole Safety
Sprague & Henwood (S&H)
Date finished: 9/29/16
Hammer weight/drop: 140 lbs./30 inches
Sampler:
K. SamlikBoring location:
Date started:
Drilling method:
Approximate Ground Surface Elevation: 192.7 feet2
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
MATERIAL DESCRIPTION
LABORATORY TEST DATA
SAMPLES
Figure:A-1a
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 1 OF 2Log of Boring B-1
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
S&H
S&H
CL
CL
SANDY CLAY (CL) (continued)
SANDY CLAY with GRAVEL (CL)yellow-brown mottled with olive-brown, hard, moist,fine to medium sand
33
39
121928
162134
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
50
51
52
53
54
55
56
57
58
59
60
MATERIAL DESCRIPTION
LABORATORY TEST DATASAMPLES
Figure:A-1b
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 2 OF 2Log of Boring B-1
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
Boring terminated at a depth of 40 feet below ground surface.Boring backfilled with cement grout.Groundwater not encountered during drilling.
1 S&H blow counts for the last two increments were convertedto SPT N-Values using a factor of 0.7 to account for samplertype and hammer energy.
2 Ground surface elevation estimated from TopographicsSurvey by Sandis, revised January 26, 2017. City of Berkeleydatum.
1071,800TxUU 21.84,300
S&H
S&H
S&H
S&H
S&H
S&H
S&H
SP
CL
SC
CL
CL
CL
CL
CL
4 inches of asphalt concreteSAND with GRAVEL (SP)light brown, medium dense, moist, angular finegravelSANDY CLAY (CL)dark brown, very stiff, moistCLAYEY SAND (SC)dark brown, medium dense, moist, fine sandSANDY CLAY (CL)brown, very stiff, moist, fine to medium sand, tracefine gravel
SANDY CLAY with GRAVEL (CL)brown mottled with yellow, hard, moist, angular finegravel, fine to coarse sand, trace rootlets
CLAY (CL)olive-brown and yellow with black staining, very stiff,moist
TxUU Test; see Appendix B
SANDY CLAY with GRAVEL (CL)olive-brown mottled with yellow, very stiff, moist,oxidized fine subrounded gravel, fine gravel-sizesandstone fragments
CLAY with SAND (CL)yellow-brown mottled with olive, very stiff to hard,moist, fine sand, trace subangular fine gravel
very stiff
27
22
67
28
20
30
18
151623
151516384550
81723
91117
41627
71213
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
See Site Plan, Figure 2
9/29/16
Hollow-Stem
Logged by:
Hammer type: Downhole Safety
Sprague & Henwood (S&H)
Date finished: 9/29/16
Hammer weight/drop: 140 lbs./30 inches
Sampler:
K. SamlikBoring location:
Date started:
Drilling method:
Approximate Ground Surface Elevation: 192 feet2
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
MATERIAL DESCRIPTION
LABORATORY TEST DATA
SAMPLES
Figure:A-2a
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 1 OF 2Log of Boring B-2
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
S&H
S&H
CL
CL
CLAY with SAND (CL) (continued)
SANDY CLAY with GRAVEL (CL)yellow-brown mottled with olive and brown, hard,moist, subrounded fine gravel, fine to medium sand
yellow-brown mottled with olive, brown, and red
47
41
152740
111643
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
50
51
52
53
54
55
56
57
58
59
60
MATERIAL DESCRIPTION
LABORATORY TEST DATASAMPLES
Figure:A-2b
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 2 OF 2Log of Boring B-2
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
Boring terminated at a depth of 40 feet below ground surface.Boring backfilled with cement grout.Groundwater not encountered during drilling.
1 S&H blow counts for the last two increments were convertedto SPT N-Values using a factor of 0.7 to account for samplertype and hammer energy.
2 Ground surface elevation estimated from TopographicsSurvey by Sandis, revised January 26, 2017. City of Berkeleydatum.
102
92
20.8
30.081
S&H
S&H
S&H
S&H
S&H
S&H
S&H
CL
CL
CL
CL
CL
4 inches of asphalt concrete8 inches of aggregate baseSANDY CLAY (CL)dark brown mottled with yellow, medium stiff, moist,fine to medium sandLL = 37, PI = 21; see Appendix B
SANDY CLAY with GRAVEL (CL)brown mottled with orange and black, very stiff,moist, fine sand, angular fine gravel
brown
subrounded fine gravel
SANDY CLAY (CL)light brown, stiff, moist, fine to medium sand, tracesubangular gravel
(2:30 PM; 9/29/16)
CLAY with SAND (CL)brown and olive, stiff to very stiff, wet, fine to coarsesandParticle Size Distribution; see Appendix BLL = 36, PI = 16; see Appendix Bolive-brown, fine to medium sand
SANDY CLAY (CL)yellow-brown, very stiff, wet, fine to medium sand,trace subrounded fine gravel
6
21
22
21
14
15
16
345
4822
111715
81317
6911
51011
6914
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
See Site Plan, Figure 2
9/29/16
Hollow-Stem
Logged by:
Hammer type: Downhole Safety
Sprague & Henwood (S&H)
Date finished: 9/29/16
Hammer weight/drop: 140 lbs./30 inches
Sampler:
K. SamlikBoring location:
Date started:
Drilling method:
Approximate Ground Surface Elevation: 194 feet2
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
MATERIAL DESCRIPTION
LABORATORY TEST DATA
SAMPLES
Figure:A-3a
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 1 OF 2Log of Boring B-3
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
S&H
S&H
CL
CL
SANDY CLAY (CL) (continued)
SANDY CLAY with GRAVEL (CL)yellow mottled with olive and brown, hard, wet,subrounded fine gravel
33
36
141730
141735
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
50
51
52
53
54
55
56
57
58
59
60
MATERIAL DESCRIPTION
LABORATORY TEST DATASAMPLES
Figure:A-3b
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 2 OF 2Log of Boring B-3
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
Boring terminated at a depth of 40 feet below ground surface.Boring backfilled with cement grout.Groundwater encountered at a depth of 21 feet after leavingthe boring open for about 3 hours.
1 S&H blow counts for the last two increments were convertedto SPT N-Values using a factor of 0.7 to account for samplertype and hammer energy.
2 Ground surface elevation estimated from TopographicsSurvey by Sandis, revised January 26, 2017. City of Berkeleydatum.
10016.6
45
S&H
S&H
S&H
S&H
S&H
S&H
S&H
SC
CL
CL
CL
SC
CL
3 to 4 inches of asphalt concrete9 inches of aggregate baseCLAYEY SAND with GRAVEL (SC)brown mottled with orange, medium dense, moist,fine to medium sand, trace angular fine gravelCorrosion Test; see Appendix BLL = 34, PI = 16; see Appendix B
dark brown mottled with yellow and red, subroundedfine gravelParticle Size Distribution; see Appendix B
SANDY CLAY with GRAVEL (CL)brown mottled with yellow and red, very stiff, moist,subangular fine gravel
CLAY (CL)brown mottled with olive, very stiff, moist
CLAY with SAND (CL)yellow-brown mottled with olive and orange, stiff tovery stiff, moist, fine sand, trace subrounded finegravel
CLAYEY SAND (SC)olive mottled with orange and brown, medium dense,moist, fine to medium sand
SANDY CLAY with GRAVEL (CL)yellow-brown mottled with olive and red, very stiff,moist, subrounded to angular fine gravel, fine tomedium sand
hard
13
25
18
29
15
28
36
10109
131619
101115
81625
7814
111822
171933
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
See Site Plan, Figure 2
9/30/16
Hollow-Stem
Logged by:
Hammer type: Downhole Safety
Sprague & Henwood (S&H)
Date finished: 9/30/16
Hammer weight/drop: 140 lbs./30 inches
Sampler:
K. SamlikBoring location:
Date started:
Drilling method:
Approximate Ground Surface Elevation: 196.1 feet2
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
MATERIAL DESCRIPTION
LABORATORY TEST DATA
SAMPLES
Figure:A-4a
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 1 OF 2Log of Boring B-4
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
S&H
S&H
CL
SC
CL
SC
SANDY CLAY with GRAVEL (CL) (continued)
CLAYEY SAND (SC)light brown, very dense, moist, fine sand, tracegravel-sized sandstone fragments
SANDY CLAY (CL)dark brown and light brown, hard, moist, fine sand
(9/30/16)CLAYEY SAND (SC)brown, very dense, wet, fine to medium sand
60
35/5"
203550
50/5"
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
50
51
52
53
54
55
56
57
58
59
60
MATERIAL DESCRIPTION
LABORATORY TEST DATASAMPLES
Figure:A-4b
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 2 OF 2Log of Boring B-4
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
Boring terminated at a depth of 39 feet below ground surface.Boring backfilled with cement grout.Groundwater encountered at a depth of 38 feet during drilling.
1 S&H blow counts for the last two increments were convertedto SPT N-Values using a factor of 0.7 to account for samplertype and hammer energy.
2 Ground surface elevation estimated from TopographicsSurvey by Sandis, revised January 26, 2017. City of Berkeleydatum.
991,800TxUU 26.63,450
S&H
S&H
S&H
S&H
S&H
S&H
S&H
S&H
CL
CL
CL
CL
CL
CL
3 inches of asphalt concrete9 inches of aggregate baseSANDY CLAY (CL)dark brown, medium stiff to stiff, fine sand, tracesubrounded fine gravel, trace rootletsSANDY CLAY with GRAVEL (CL)brown, very stiff, moist, fine to coarse sand, angularfine gravel
Corrosion Test; see Appendix Bbrown mottled with red and yellow, subangular finegravel
CLAY with SAND (CL)olive-brown mottled with yellow, very stiff, moist, finesandTxUU Test; see Appendix B
CLAY with SAND (CL)yellow-brown with red and black staining, very stiff,moist, fine sand, trace subangular fine gravel
SANDY CLAY (CL)yellow-brown mottled with olive, very stiff to hard,moist, fine to medium sand
SANDY CLAY with GRAVEL (CL)yellow-brown, hard, moist, fine to medium sand,subangular fine gravel
8
18
28
20
18
23
29
49
456
91016
101624
81217
71115
71320
51626
153040
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
See Site Plan, Figure 2
9/30/16
Hollow-Stem
Logged by:
Hammer type: Downhole Safety
Sprague & Henwood (S&H), Standard Penetration Test (SPT)
Date finished: 9/30/16
Hammer weight/drop: 140 lbs./30 inches
Sampler:
K. SamlikBoring location:
Date started:
Drilling method:
Approximate Ground Surface Elevation: 194.1 feet2
1
2
3
4
5
6
7
8
9
10
11
12
13
14
15
16
17
18
19
20
21
22
23
24
25
26
27
28
29
30
MATERIAL DESCRIPTION
LABORATORY TEST DATA
SAMPLES
Figure:A-5a
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 1 OF 2Log of Boring B-5
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
S&H
S&H
SPT
SPT
SC
SC
CL
SANDY CLAY with GRAVEL (SC) (continued)
yellow-brown mottled with olive, brown and orange
(9/30/16)
CLAYEY SAND with GRAVEL (SC)yellow-brown mottled with olive and brown, verydense, wet, fine to medium sand, subangular finegravel
CLAY (CL)brown mottled with olive, hard, wet, trace fine sand
40
31
48
32
152433
101628
81624
101017
Dry
Den
sity
Lbs/
Cu
Ft
Type
of
Stre
ngth
Test
She
ar S
treng
thLb
s/S
q Ft
Fine
s%
Con
finin
gP
ress
ure
Lbs/
Sq
Ft
Nat
ural
Moi
stur
eC
onte
nt, %
Sam
pler
Type
Sam
ple
Blo
ws/
6"
SP
TN
-Val
ue1
LITH
OLO
GY
DE
PTH
(feet
)
31
32
33
34
35
36
37
38
39
40
41
42
43
44
45
46
47
48
49
50
51
52
53
54
55
56
57
58
59
60
MATERIAL DESCRIPTION
LABORATORY TEST DATASAMPLES
Figure:A-5b
PROJECT:
Project No.:16-1193
2012 BERKELEY WAYBerkeley, California
PAGE 2 OF 2Log of Boring B-5
RO
CK
RID
GE
16-
1193
.GP
J T
R.G
DT
3/2
4/17
Boring terminated at a depth of 50 feet below ground surface.Boring backfilled with cement grout.Groundwater encountered at a depth of 43 feet during drilling.
1 S&H and SPT blow counts for the last two increments wereconverted to SPT N-Values using factors of 0.7 and 1.2,respectively, to account for sampler type and hammerenergy. SPT sampler used without liners.
2 Ground surface elevation estimated from TopographicsSurvey by Sandis, revised January 26, 2017. City of Berkeleydatum.
CLASSIFICATION CHART
Major Divisions Symbols Typical Names
GW
GP
GM
GC
SW
SP
SM
SC
ML
CL
OL
MH
CH
OH
PTHighly Organic Soils
UNIFIED SOIL CLASSIFICATION SYSTEM
Well-graded gravels or gravel-sand mixtures, little or no fines
Poorly-graded gravels or gravel-sand mixtures, little or no fines
Silty gravels, gravel-sand-silt mixtures
Clayey gravels, gravel-sand-clay mixtures
Well-graded sands or gravelly sands, little or no fines
Poorly-graded sands or gravelly sands, little or no fines
Silty sands, sand-silt mixtures
Inorganic silts and clayey silts of low plasticity, sandy silts, gravelly silts
Inorganic clays of low to medium plasticity, gravelly clays, sandy clays, lean clays
Organic silts and organic silt-clays of low plasticity
Inorganic silts of high plasticity
Inorganic clays of high plasticity, fat clays
Organic silts and clays of high plasticity
Peat and other highly organic soils
Clayey sands, sand-clay mixtures
Range of Grain SizesGrain Size
in MillimetersU.S. Standard
Sieve SizeAbove 12"
12" to 3"
Classification
Boulders
Cobbles
Above 305
305 to 76.2
Silt and Clay Below No. 200 Below 0.075
GRAIN SIZE CHART
SAMPLER TYPE
Coa
rse-
Gra
ined
Soi
ls(m
ore
than
hal
f of s
oil >
no.
200
siev
e si
ze)
Fine
-Gra
ined
Soi
ls(m
ore
than
hal
f of s
oil
< no
. 200
sie
ve s
ize)
Gravels(More than half ofcoarse fraction >no. 4 sieve size)
Sands(More than half ofcoarse fraction <no. 4 sieve size)
Silts and ClaysLL = < 50
Silts and ClaysLL = > 50
Gravel coarse fine
3" to No. 43" to 3/4"
3/4" to No. 4
No. 4 to No. 200No. 4 to No. 10No. 10 to No. 40No. 40 to No. 200
76.2 to 4.7676.2 to 19.119.1 to 4.76
4.76 to 0.0754.76 to 2.002.00 to 0.4200.420 to 0.075
Sand coarse medium fine
C Core barrel
CA California split-barrel sampler with 2.5-inch outside diameter and a 1.93-inch inside diameter
D&M Dames & Moore piston sampler using 2.5-inch outside diameter, thin-walled tube
O Osterberg piston sampler using 3.0-inch outside diameter, thin-walled Shelby tube
PT Pitcher tube sampler using 3.0-inch outside diameter, thin-walled Shelby tube
S&H Sprague & Henwood split-barrel sampler with a 3.0-inch outside diameter and a 2.43-inch inside diameter
SPT Standard Penetration Test (SPT) split-barrel sampler with a 2.0-inch outside diameter and a 1.5-inch inside diameter
ST Shelby Tube (3.0-inch outside diameter, thin-walled tube) advanced with hydraulic pressure
SAMPLE DESIGNATIONS/SYMBOLS
Sample taken with Sprague & Henwood split-barrel sampler with a 3.0-inch outside diameter and a 2.43-inch inside diameter. Darkened area indicates soil recovered
Classification sample taken with Standard Penetration Test sampler
Undisturbed sample taken with thin-walled tube
Disturbed sample
Sampling attempted with no recovery
Core sample
Analytical laboratory sample
Sample taken with Direct Push sampler
Sonic
Unstabilized groundwater level
Stabilized groundwater level
ROCKRIDGEGEOTECHNICAL Project No. Figure A-6Date 16-119311/21/16
2012 BERKELEY WAYBerkeley, California
APPENDIX B Laboratory Test Results
ML or OL
MH or OH
Symbol SourceNatural
M.C. (%)Liquid
Limit (%)
CL - ML
0
10
20
30
40
50
60
70
0 10 20 30 40 50 60 70 80 90 100 110 120LIQUID LIMIT (LL)
Description and Classification% Passing#200 Sieve
PlasticityIndex (%)
PLASTICITY CHART
ROCKRIDGEGEOTECHNICAL Project No. FigureDate B-116-119311/21/16
2012 BERKELEY WAYBerkeley, California
PLA
STI
CIT
Y IN
DE
X (P
I)Ref erence:ASTM D2487-00
B-3 at 24 feet
B-3 at 2.0 feet
B-4 at 1.5 feet
CLAY with SAND (CL), brown and olive
SANDY CLAY (CL), dark brown mottledwith yellow
CLAYEY SAND with GRAVEL (SC),brown mottled with orange
30.0
20.8
16.6
81
--
--
35
37
34
16
21
16
SYMBOL SOURCE DEPTH Material Description USCS(ft.)
MATERIAL DATA
PE
RC
EN
T FI
NE
R
0
10
20
30
40
50
60
70
80
90
100
GRAIN SIZE - mm.
0.0010.010.1110100
% +3"Coarse
% GravelFine Coarse Medium
% SandFine Silt
% FinesClay
6 in
.
3 in
.
2 in
.1½
in.
1 in
.¾
in.
½ in
.3/
8 in
.
#4 #10
#20
#30
#40
#60
#100
#140
#200
B-1 5.5'
B-3
B-4 6.0'
PARTICLE SIZE DISTRIBUTION REPORT
ROCKRIDGEGEOTECHNICAL
SANDY CLAY with GRAVEL, brown with yellow and orange
CLAY with SAND, brown and olive
CLAYEY SAND with GRAVEL, brown mottled with orange
Project No. FigureDate B-216-1193
24.0’
CL
CL
SC
11/21/16
2012 BERKELEY WAYBerkeley, California
0
1,000
2,000
3,000
4,000
5,000
6,000
7,000
8,000
9,000
10,000
0 5 10 15 20 25
Project No. FigureDate B-3
UNCONSOLIDATED-UNDRAINEDTRIAXIAL COMPRESSION TEST
ROCKRIDGEGEOTECHNICAL
B-2 at 14.5 feetCLAY (CL), olive-brown
2.40 5.65
21.8
107
4,300
20.0
1,800
1
SAMPLER TYPE
DIAMETER (in.)
MOISTURE CONTENT
DRY DENSITY
DESCRIPTION
SHEAR STRENGTH
STRAIN AT FAILURE
CONFINING PRESSURE
STRAIN RATE
HEIGHT (in.)
SOURCE
%
pcf
psf
%psf
% / min.
AXIAL STRAIN (percent)
Sprague and Henwood
DE
VIA
TOR
STR
ES
S (p
sf)
16-119311/21/16
2012 BERKELEY WAYBerkeley, California
0
1,000
2,000
3,000
4,000
5,000
6,000
7,000
8,000
0 5 10 15 20 25
Project No. FigureDate B-4
UNCONSOLIDATED-UNDRAINEDTRIAXIAL COMPRESSION TEST
ROCKRIDGEGEOTECHNICAL
B-5 at 14.5 feetCLAY with SAND (CL), olive-brown mottled with yellow
2.39 5.98
26.6
99
3,450
17.9
1,800
1
SAMPLER TYPE
DIAMETER (in.)
MOISTURE CONTENT
DRY DENSITY
DESCRIPTION
SHEAR STRENGTH
STRAIN AT FAILURE
CONFINING PRESSURE
STRAIN RATE
HEIGHT (in.)
SOURCE
%
pcf
psf
%psf
% / min.
AXIAL STRAIN (percent)
Sprague and Henwood
DE
VIA
TOR
STR
ES
S (p
sf)
16-119311/21/16
2012 BERKELEY WAYBerkeley, California