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Application of Natural Laminar Flow to a Supersonic Transport Concept (AIAA-1993-3467-139)
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APPLICATION OF NATURAL LAMINAR FLOW TO A SUPERSONIC TRANSPORT CONCEPT
Henri D. Fuhrmann*
NASA Langley Research Center
Hampton, Virginia 23681-0001
Abstract
Results are presented of a preliminary investigation
into an application of supersonic natural laminar flow
(NLF) technology for a high speed civil transport
(HSCT) configuration. This study focuses on natural
laminar flow without regard to suction devices which
are required for laminar flow control (LFC) or hybrid
laminar flow control (HLFC). An HSCT design is
presented with a 70' inboard leading-edge sweep and
a 20" leading-edge outboard crank to obtain NLF overthe outboard crank section. This configuration takes
advantage of improved subsonic performance and
NLF on the low-sweep portion of the wing while
minimizing the wave drag and induced drag penalties
associated with low-sweep supersonic cruise aircraft.
In order to assess the benefits of increasing natural
laminar flow wetted area, the outboard low-sweep
wing area is parametrically increased. Using a range of
supersonic natural laminar flow transition Reynolds
numbers, these aircraft are then optimized and sized
for minimum take-off gross weight (TOGW) subject to
mission constraints. Results from this study indicate
reductions in TOGW for the NLF concepts, due mainlyto reductions in wing area and total wing weight.
Furthermore, significant reductions in block fuel are
calculated throughout the range of transition Reynolds
numbers considered. Observations are made on the
benefits of unsweeping the wingtips with all turbulent
flow.
Nomenclature
A 2 I A ~ Ratio of the outboard wing area to
total theoretical wing area
CL Lift coefficient
CD Drag coefficientC D ~ Nacelle base drag coefficient
CDW Wave drag coefficientFLOPS Flight optimization system
FN/WGTO Take-off thrust-to-weight ratio
-* ~ e r o s ~ a c engineer, member AIAA
HLFC
HSCT
LFC
L/DM
NLF
n.m.
Rtr
swTBE
TOFL
Hybrid laminar flow control
High speed civil transport
Laminar flow control
Lift-to-drag ratio
Free-stream Mach number
Natural laminar flow
Nautical miles
Transition Reynolds number
Wing reference area
Turbine bypass engine
Take-off field lengthTOGW Take-off gross weight
TOGW/TOGWA Take-off gross weight normalized
to that of reference arrow-wing
Ww/WWA Wing weight normalized to that of
reference arrow-wing
Introduction
The National Aeronautics and Space Administration
(NASA) has recently begun to focus on high-speed
research with the intent of providing the technology
for an economically viable commercial supersonictransport to be certified around the year 2005.' By the
year 2015, more than 600,000 passengers a day are
expected to be flying on the long, over-water routes
that a supersonic transport could economically serve.2
The United States must act decisively to capture this
lucrative market and bolster the positive balance of
trade generated by the aerospace industry. In order to
help U.S. companies produce an aircraft that will be
both economically viable and environmentally
compatible, NASA must consider and examine all
promising technologies and the advantages they may
offer for supersonic flight.
Supersonic transport wing concepts have evolved into
highly efficient cranked wing planform designs. These
planforms consist of an inboard section with a
subsonic leading edge swept behind the local Mach
angle, and an outer panel of reduced sweep to enhance
low-speed stability and performance. The highly
swept inboard section achieves high aerodynamic
efficiency at cruise because of its subsonic leading edgeCopyri htO 1993 y the American Institute of Aeronautics and Astronautics Inc. Nomp yr ia t is asserted in the United States under Title 17 U.S. Code. The U.S. Governmenthas a royak free license to ex8rcis.e all rights under the'copyright claimed herein for~ov ern me nri l urposes. All other r~ghts re reserved by the wpyr~g ht wner.
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which also allows for thicker chord sections for good
structural efficiency and increased volume for fuel
tanks. However, the outer wing panel must be
designed with a sharp leading edge and very thin wing
sections because the reduced leading edge sweep of
about 40 to 45" results in a supersonic leading edge at
cruise.
Promising techniques to further improve supersonic
cruise performance by reducing skin friction drag
through laminar flow technology are being explored.
In recent years, the practical benefits of laminar flow
for reducing drag have been demonstrated for
subsonic speeds both in wind tunnels and on flight
e ~ ~ e r i m e n t s ? ~ ~ ~upersonic laminar flow offers
significant reductions in drag, skin temperature,
structural weight, thermal insulation and noise
in~ula t ion .~f~he available data suggest that the high
cross-flow instability characteristic of highly swept
wings makes laminar flow impractical without laminarflow control (LFC) devices such as suction.819110
Typical supersonic transport concepts have highly
swept leading edges; therefore, current research thrusts
have primarily focused on the application of laminar
flow control with its attendant suction devices. It
might be possible, however, to induce natural laminar
flow (NLF) over the outboard cranked portion of the
typical arrow wing design if the outboard wing section
were not swept to the extent currently being
considered. While it is true that reducing wing sweep
may adversely affect supersonic aerodynamic
performance; there may be benefits that must also be
considered such as reduced skin friction due to NLFand improved subsonic performance. Therefore, an
overall system study is necessary to fully assess the
benefits of a partial low-sweep HSCT designed for
NLF and is the subject of this paper.
Supersonic natural laminar flow on low-sweep wings
does in fact hold promise. In 1958, flight experiments
conducted on a modified F-104 aircraft examin-ed the
extent to which supersonic natural laminar flow could
be obtained." The F-104 has a wing leading-edge
sweep of 26.9" and flew at Mach numbers between 1.2
and 2.0 at altitudes from 30,000 to 55,000 feet. A
transition Reynolds number of up to 8 or 9 million andabout 35% chord had beer. obtained. Despite this
success, little work in the area of supersonic natural
laminar flow has been accomplished.
The supersonic natural laminar flow aircraft concept
analyzed in this study is a modification of a baseline
cranked arrow-wing configuration which has a 70"
leading-edge sweep on the inboard portion of the wing
and a 45" leading-edge sweep on the outboard portio
of the wing. This 70°-45" planform configuration
optimized for a Mach 2 mission. The modifications f
the NLF concept include a reduction in outboard win
sweep to 20" to take advantage of natural laminar flo
by minimizing the cross-flow instability. The ratio
the outboard wing area to total theoretical wing are(A2/AT)is parametrically varied from 0.23 to 0.4 an
each aircraft is individually optimized and sized
four transition Reynolds numbers from 0 to 30 millio
This paper presents the mission analysis results of th
parametric set of 70"-20" HSCT configurations subje
to a range of transition Reynolds numbers as well
all-turbulent flow. A reference 70°-45" cranked arrow
wing HSCT optimized and sized for the same missio
using consistent methods and assumptions is als
presented as a baseline. The aerodynamic performan
is evaluated, configuration modifications a
documented, and normalized gross take-off weigcomparisons are presented for the configurations.
an effort to evaluate the advantages NLF alone ma
hold, suction devices were not considered in this stud
The results suggest that a partial low-sweep design f
supersonic natural laminar flow may offer advantag
over a typical cranked arrow-wing with turbulent flo
Laminar flow is the smooth flow velocity transitio
within the boundary layer from the surface of th
aircraft to the local free-stream velocity resulting insignificant reduction in skin friction drag. The amou
of laminar flow wetted area present on an aircra
depends on the transition Reynolds number (Rk). T
transition Reynolds number of concern for this study
the Reynolds number at which the boundary lay
flow will transition from laminar to turbulent witho
the aid of active devices for prolonging laminar flo
This natural laminar flow transition Reynolds numb
is used as a basis for determining how much lamin
flow wetted area can be obtained naturally.
Factors such as surface tolerance, cruise Mach numb
and wing sweep affect the transition Reynolds numbin various ways. First, any surface designed f
laminar flow must be very smooth and free from step
gaps, rivets, and insects which may prematurely tr
the laminar boundary layer to turbulent flow. The
factors are hard to quantify but will degrade ide
performance and become important when consideri
manufacturing and maintenance issues. Second, for
given airfoil and chord Reynolds number, t
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transition Reynolds number (R,,) generally increases
with increasing Mach number. This has been
demonstrated both in flight and in wind-tunnel tests.'*
Finally and most importantly, the transition Reynolds
number decreases significantly with increasing wing
sweep. This is a result of the cross-flow instabilities
that are generated by highly swept wings. Figure I
from reference 13 demonstrates the effect of sweep on
the natural laminar flow transition Reynolds number.
The figure shows transition Reynolds number versus
wing sweep for various subsonic and supersonic wind-
tunnel and flight test data points. The dotted line
represents the current limit of natural laminar flow that
has been obtained to date. Above this limit, suction
devices have and must be used in order to increase the
transition Reynolds number. It is evident from the
available data and compressible stability theory that in
order to maximize the natural laminar flow transition
Reynolds number and, therefore, the amount of
natural laminar flow wetted area, a low-sweep wing
design with a leading-edge sweep of about 20" or
below is needed.
Research in the area of low-sweep supersonic natural
laminar flow in a pressure gradient is virtually
nonexistent. The effect of tunnel noise on transition
has rendered data obtained in other than quiet wind-
tunnels suspect.14 The trends obtained in these tunnels
are usually correct but the absolute transition Reynolds
numbers have been found to be about half of that
obtained in flight.15 The result is that a consensus or
valid data base does not exist for the accurate
prediction of the natural transition Reynolds number
that would be obtained on an airfoil at supersonic
speeds. Based on flight tests, quiet tunnel tests, trends,
and compressible stability theory, a range of possible
transition Reynolds numbers has been selected for this
study.
The range of supersonic natural laminar flow
transition Reynolds numbers considered for this study
is 10, 20, and 30 million. The lower value chosen is
based on the results, though not precisely documented,
of the P-104 flight test; the midrange is based on the
natural laminar flow limit trend presented in figure 1;and the high value is an optimistic look at the benefits
of NLF. It is important to note that whether one is
considering NLF, LFC or HLFC, an in-depth
knowledge of the transition Reynolds number is
needed. In order to make accurate design predictions
and perform laminar flow concept studies, research in
this area, preferably in the form of flight experiments,
must continue.
Mission Definition
The HSCT mission chosen is a typical transpacific
route.16117The aircraft is to carry 248 passengers and a
crew of 9 at a cruise Mach number of 2.0 for 5500
nautical miles with a 4.5% fuel reserve and a 250 n.m.
subsonic alternate airport capability. The take-off and
landing field lengths are limited to 12000 feet and FAR
engine-out second-segment climb and missed
approach performance parameters are required.
Approach speed is limited to 160 knots. No noise
restrictions are considered for aircraft sizing and no
over land supersonic flight or supersonic boom
considerations are examined.
The effect of take-off and landing noise on wing area
and engine thrust-to-weight sizing is not considered
although it has been found to be a determining factor
in aircraft sizing. These factors as well as different
take-off and landing field length restrictions and
approach velocities will influence the sizing results
presented in this paper, however, these factors are not
examined in this study.
The 70"-45"Baseline Reference Confieuration
The 70"-45" baseline configuration presented in figure
2 is modeled after typical cranked arrow-wing HSCT
designs with a highly efficient subsonic leading edge
on the inboard portion of the wing, and an outboard
cranked section for improved take-offperformance.18119~20 The outboard crank results in a
supersonic leading edge at cruise. The ratio (t/c ) of
wing thickness to chord along the span of the wing is
0.03 at the root and midspan tapering to 0.015 at the
wing tip. The fuselage of the aircraft is 295 feet long
with varying cross-sectional area for wave-drag
minimization. Seating is arranged in sections of four,
five, and six abreast depending on the cross-sectional
area. Sufficient room is allocated for exits, lavatories,
galleys, aisles, and passenger seating. Fuel is
contained primarily in the wing but also in a fuselage
tank located aft of the passenger compartment. This
tank may also be used for trim purposes. Landing gearare stowed in the wing and belly of the aircraft with
loss of fuel volume considerations taken into account.
Some highly advanced technology and composite
factors projected to become available are employed
and used consistently throughout the study. This
baseline configuration is sized with the same
methodology used for the rest of the study.
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Encine Specifications
The engine employed in this study is a generic
advanced technology turbine bypass engine (TBE)
based on early NASA engine technology
projections.2' This engine operates as a turbojet engine
with a bypass valve that allows the TBE cycle tomaintain constant turbine corrected airflow
throughout the flight envelope without the need to
vary throttle setting. A higher specific thrust is
obtained by allowing a minimal amount of compressor
discharge air to pass around the combustor and
turbines allowing for higher cycle pressures and
temperatures to be achieved. The net effect of the
turbine bypass engine is high specific thrust at
sustained airflows resulting in less spillage and boattail
drag. This engine has been used in the studies of
references 19 and 20 and is consistently used for all of
the aircraft presented in this study.
The 70"-20" Suversonic Transport Confipra tio n
The 70"-20" aircraft configuration presented here in
figure 3 is designed to utilize natural laminar flow
while minimizing any penalties associated with low-
sweep designs. The configuration is based on the 70"-
45" cranked arrow wing HSCT with minimal
modifications for consistent comparisons. The
outboard wing sweep is reduced to 20" to support NLF
and the thickness of this low-sweep portion of the
wing is reduced to minimize wave drag. The thickness
to chord ratio of the wing is 0.03 at the wing root and
varies from 0.03 at the root of the low-sweep sectionto 0.015 at the tip. The highly swept inboard section
cannot support NLF as a result of the cross-flow
instabilities and would require suction if laminar flow
were desired on this area. This study does not consider
any such LFC combinations. The very thin wing and
sharp supersonic leading edge are similar to that of the
F-104 which has demonstrated supersonic NLF in
flight. The fuselage length is the same as that of the
70"-45" baseline configuration and the body is
independently area ruled for minimum cruise wave
drag. All design considerations and assumptions
including the horizontal and vertical stabilizer
assembly, trim tank, and the turbine bypass enginesare consistent with the reference 70"-45" cranked
arrow-wing with the exception of wing fuel tanks as
discussed in the following section.
Fuel Volume Constraint Considerations And
Modifications
The reduction in wing fuel volume on the 70"-2
configuration due to the thinner outboard wing sectio
creates a problem for wing sizing. The optimizatio
and sizing trends point to benefits from a significareduction in wing area, however, the wing size
ultimately constrained by the desire to carry the fuel
wing fuel tanks. In order to relieve the fuel volum
sizing constraint, wing slipper tanks and increas
fuselage tank volume had been considered but the fin
configuration employs wing root tanks. The wing ro
is extended and the volume increased to conta
sufficient fuel in the long cylindrical fuel mks
compensate for the loss of fuel volume in the win
The volume of these root tanks remains independent
the wing area. Figure 4 gives a cross-secti
comparison of the 70"-20" configuration with the win
root tank extensions and the reference 70"-4configuration, which is able to contain all of the fuel
the wing and trim tank without exceeding the fu
volume constraint.
A similar concept for relieving the fuel volum
constraint had been employed in the studies o
references 19 and 20. This method is used in order
assess the full benefits of wing sizing for missio
constraints other than wing fuel tank volume. Th
wing root tank concept may also help in area ruling th
aircraft by varying the root tank volume as opposed
the fuselage cross-sectional area, thereby allowing for
more consistent fuselage and seating arrangement well as reduced manufacturing complexity. Oth
methods of relieving the wing fuel volume constrai
may prove more beneficial but for this study the win
root fuel tank modification proves to be sufficient. A
skin friction, wave drag, and weight penalties a
assessed for the wing fuel tank modification.
Parametric Variation
The benefits of NLF for skin friction reduction are clea
but the effect of an NLF configuration on the integrate
design of a supersonic transport is a comple
interaction of aerodynamics, propulsion and structurweight. In order to assess the benefits of variou
amounts of NLF wetted area on reducing the take-o
gross weight of this 70"-20' HSCT configuration, th
outboard low-sweep portion of the wing
parametrically increased. The ratio (AZ/AT) of th
outboard low-sweep area (A2) to the total wing are
(AT) s varied from 0.23 to 0.4. The leading and trailin
edge sweeps and outboard planform geometri
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remain constant while the aspect ratio and (A2/AT)
ratio are varied. Each of the aircraft are then resized
for minimum take-off gross weight by optimizing the
engine thrust and wing area. The three 70"-20"
configurations examined are presented in figure 5 with
the baseline cranked arrow-wing for reference. This
matrix of three configurations at four transitionReynolds numbers is analyzed and the results
compared to those of the arrow-wing configuration.
An example of the location and amount of NLF wetted
area assumed for each transition Reynolds number is
illustrated in figure 6.
Analysis Methods
A consistent design, optimization and analysis method
is used throughout this study. Using the wing and
airfoil geometry, a modified linear theory code
developed by ~ a r l s o n ~ ~s used to optimally twist andcamber the wings for minimum drag-due-to-lift at
cruise and subsequently supersonic lift dependent
drag is obtained. The thin, sharp leading edge of the
outboard low-sweep portion of the wing needs very
little twist and camber. No penalties on NLF
performance resulting from minimum drag-due-to-lift
optimization were assessed. Flap scheduling and
subsonic aerodynamic data are obtained using the
method of reference 23. Each body is optimally area
ruled for minimum cruise wave drag using the Harris
wave drag code of reference 24. This method is also
used to calculate the wave drag for each of the Mach
numbers required. Wave drag minimization at cruise
does at times cause the wave drag at lower supersonic
Mach numbers to be unacceptably high which in turn
penalizes the engine requirements for transonic
acceleration. In order to avoid sizing the engine for
transonic acceleration, a technique of minimizing wave
drag alternately at Mach 1.2 and Mach 2.0 is used. Skin
friction drag is calculated using the T-Prime method of
Sommer and Roughness drag is estimated
using empirical methods, and form drag is calculated
using geometry dependent factors such as wing chord,
camber and fuselage geometry.26
Linear theory cannot take into consideration the flow
separation that occurs as a result of high flap
deflections typical of take-off and landing. Therefore,
take-off and landing aerodynamics are based on wind-
tunnel test results of a 70"-20" fighter aircraft
The data are progressively
modified for the remaining parametric cases. The flow
visualization data from these tests are used to estimate
the NLF wetted area that may be affected by the wing
tip and vortex flow of the inboard wing section. Figure
7 shows oil flow patterns on the 70"-20" fighter model
at supersonic speeds illustrating minimal disturbance
from the areas of concern.29
The method for estimating weights uses empirically
derived weight equations developed from a data baseof transport aircraft with structural weights based on
aluminum and titanium. Incorporated in the equations
are technology factors which reflect advances in
technology, manufacturing, and materials that may
result in a weight change. Advanced structures,
controls, aerodynamics, and propulsion technologies
are projected. The wing structure for all concepts is
assumed to be primarily constructed of composite
material. Advanced subsystems for auxiliary power,
avionics, and environmental control are used and
reductions in weight on the order of 15-20 percent are
reflected in the weights of these components compared
to current subsystems. All technology factors and
projections are used consistently throughout the study.
The weight estimation equations and codes comprise
the weights module of the Flight Optimization System
( F LOPS ) . ~ ~Mission analysis and vehicle sizing
calculations are performed with the FLOPS program.
FLOPS is a multidisciplinary system of computer
programs for conceptual and preliminary design and
evaluation of advanced aircraft concepts. It consists of
five primary modules: weights, aerodynamics, mission
performance, take-off and landing, and cost. Only the
weights and mission performance modules are utilized
in this study with the aerodynamic information being
supplied by linear methods, and or experimental and
empirical data.
Results
Results are presented for the three 70"-20" NLF
configurations with area ratios (A2/AT) of 0.23, 0.3,
and 0.4 at transition Reynolds numbers (R,,) of 0, 10,
20, and 30 million. The optimized, all turbulent 70"-45"
baseline configuration is also presented for
comparison. Aerodynamic and weights informationare analyzed and presented as well as sizing and
TOGW results. Each area ratio configuration at each
transition Reynolds number is individually sized for
minimum take-off gross weight by varying wing area
and engine thrust-to-weight.
The data presented in figure 8 shows lift-to-drag ratios
versus lift coefficient for each of the sized aircraft in
take-off configuration. Comparison of the baseline
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arrow wing and 70"-20" configurations shows an
increase in take-off performance for the partial low-
sweep designs. This improvement in subsonic
performance can be attributed to the greater efficiency
of low-sweep wings and a higher aspect ratio. The
improved take-off and subsonic performance of the
70"-20" wing allows for a significant reduction in wing
area and subsequent reductions in OEW. The black
dots in figure 8 denote the take-off CLpoint for each of
the sized aircraft. The different take-off CLpoints are a
result of variations in TOGW and wing area.
Wave drag and base drag dependence on Mach
number for each of the parametric cases is presented in
figure 9. Each aircraft is individually area ruled for
minimum wave drag. The partial low-sweep designs
have increased wave drag both at low supersonic
Mach numbers and at the cruise Mach number of 2.0.
Wave drag at low supersonic Mach numbers becomes
high and begins to dominant engine sizing
requirements for increasing wing area ratios.
Therefore, it becomes necessary to perform area-rule
optimization at lower supersonic Mach numbers in
order to minimize the transonic drag peak for these
higher wing area ratio cases.
Plots of the Mach 2.0 lift-to-drag ratio versus the
coefficient of lift for each parametric case at transition
Reynolds numbers of 0, 10, 20, and 30 million are
presented in figures 10 through 13. A median cruise CL
of 0.1 is typical. The cruise performance of the 70"-20"
turbulent configurations compared to the baseline
arrow-wing are degraded. The cruise L/D improves
with higher Rt, resulting from the reduction in skin
friction drag, but L/D decreases with larger area ratios
(A2/AT) and never exceeds the performance of the
arrow-wing configuration. This A2/AT effect on cruise
performance is a result of competing skin friction,
wave drag, and drag-due-to-lift factors.
In summarizing the aerodynamic results, it is observed
that the various R, numbers and resulting amounts of
natural laminar flow assumed on the 70"-20"
configurations help to improve cruise L/D over the
turbulent cases. Increasing the area ratio above
approximately 0.25 does not help to improve the cruise
performance of the aircraft. Structurally a similar
trend is observed. Figure 14 shows the trend for the
ratio of wing weight to total theoretical wing area as a
function of area ratio A2/AT. The increasing wing
weight trend is a result of a thinner outboard wing
section, reduction in fuel for load alleviation, and
higher wing loading. Figure 15 shows the wing area
for each configuration, and figure 16 presents the non-
dimensional wing weight trend. Although the wing of
the 70"-20" configurations size considerably smaller
than the arrow-wing, the normalized wing weight
begins to increase significantly with increasing area
ratio resulting in a higher OEW.
Engine sizing does not prove to be critical once the
issue of low Mach number wave drag is corrected. The
engines are sized for TOFL and second segment climb
excess thrust. Figure 17 shows the aircraft thrust to
weight ratio (FN/WGTO) for each configuration.
Overall improvements in take-off performance are
reflected in the reduction of take-off thrust loading of
the partial low-sweep configurations over the arrow-
wing. In general, thrust loading is relatively
insensitive to the parameters investigated in this study.
The individual structural and aerodynamic results
affect sizing of the aircraft based on the mission
constraints. Figures 18-21 are breakdowns of the
normalized gross take-off weight showing the payload,
operational empty weight (OEW), block fuel and
reserve fuel. A reduction in TOGW for the all
turbulent flow 70"-20" configuration is observed, but
increasing A2/AT above 0.23 results in higher OEW
and TOGW (Fig. 18). The subsequent figures are for
the 10, 20, and 30 million transition Reynolds number
cases. Again, the sizing results show a reduction in
take-off gross weight (TOGW) for the 70"-20"
configurations. This OEW reduction is a result of
smaller wing areas needed for take-off. Reductions in
reserve fuel and block fuel as a result of the improved
subsonic performance and reduced TOGW are also
observed.
The normalized TOGW versus area ratio for each
transition Reynolds number is presented in figure 22.
This figure demonstrates a large reduction in TOGW
with increasing transition Reynolds number. The
minimum TOGW is found near an area ratio of about
0.23 at the lower transition Reynolds numbers. This
bucket occurs because of the trades between the
aerodynamic and structural results previously
discussed. Increasing transition Reynolds number for
a given configuration lowers block fuel needed and
results in lower TOGW. However, increasing the area
ratio much beyond 0.3 even for the higher transition
Reynolds number cases does not prove favorable for
the 70"-20" configuration within the range of transition
Reynolds numbers assumed, although reductions in
block fuel for these higher transition Reynolds
numbers are calculated. Increasing the ratio of
outboard wing area to total wing area beyond 0.3
always has the effect of increasing the wing weight and
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OEW without significantly improving performance,
thereby resulting in a higher TOGW. For this study the
trends appear to be nearly independent of transition
Reynolds number.
The results show that a reduction in operational empty
weight is realized on the all-turbulent 70"-20" crankedarrow-wing configuration. This is a direct result of the
improved take-off performance which allows the wing
size and wing weight to be reduced. Furthermore,
improvements in subsonic performance help to further
reduce TOGW by reducing the amount of reserve fuel
which must be carried throughout the mission. Finally,
the effects of natural laminar flow result in significant
block fuel reductions. Overall, improvements are
obtained both from the implementation of the 70"-20'
wing and the natural laminar flow skin friction
reduction on the low-sweep portion.
Conclusions
Laminar flow may hold promise for efficient
supersonic cruise in future aircraft. Research in the
area of LFC and HLFC continues but supersonic NLF
work remains virtually nonexistent. As a result, little is
known about the amount of NLF that can be expected
in flight and the benefits that may be obtained. This
study was initiated to explore the possibility of
improving supersonic transport performance through
the application of NLF. The system study analysis of a
70'-20 supersonic transport concept with natural
laminar flow over the outboard low-sweep wing panel
reveals significant benefits. Conclusions from thisstudy are:
1) Natural laminar flow may offer benefits for
supersonic transport aircraft through reduced take-off
gross weight and fuel requirements. Continued
examination of supersonic NLF aircraft concepts and
transition Reynolds number phenomena appears
warranted.
2) Reductions in operational empty weight and fuel
weight of a 70"-20" natural laminar flow HSCT
configuration compared to a typical cranked (70"-45")
arrow-wing baseline have been shown. Weight
reductions occur primarily from a reduction in wing
area resulting from improved subsonic performance.
This was possible only by locating the fuel in wing root
tank extensions.
3) The 70"-20" HSCT configuration also demonstrates
a lower gross take-off weight compared to the baseline
arrow-wing even for all turbulent flow. This again is
primarily due to smaller wing area requirements and is
made possible only by the placement of fuel in root
tank modifications.
4) Wing area and engine thrust trades show that the
optimum ratio of outboard wing area to total
theoretical wing area is about 0.25 for the range oftransition Reynolds numbers (0,10,20, and 30 million)
and mission constraints considered in this study.
5) Higher transition Reynolds numbers result in
reduced take-off gross weight primarily due to
reductions in both cruise and reserve fuel
requirements.
References
1. Aviation Week and Space Technology.
December 14/21, 1992. "Goldin Defines Policy to
Reinvigorate Aeronautics Research,
Infrastructure." pp. 70-71.
2. Rosen, Robert; and Williams, Louis J.: TheRebirth of Superson ic Transport . Technology Review,
February/March 1993, pp. 22-29.
3. Harris, Charles D.; Harvey, William D.; and
Brooks, Cuyler W., Jr.: The NA S A Langley Laminar-
Flow-Control Experiment on a Swept, SupercriticalAirfoil. NASA TP 2809,1988.
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and Aeronautics, vol. 4, no. 7, July 1966.
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6. Bushnell, D.: Supersonic Aircraft Drag Reduction.AIAA 21st Fluid Dynamics, Plasma Dynamics and
Lasers Conference. June 1990.
7. Powell, A. G.; Agrawal, S.; and Lacey, T. R.:
Feasibility and Benefits of Laminar Flow Control onSupersonic C ruise Airplanes. NASA CR 181817, July
1989.
8. Chapman, Gary T.: Some Effects of Leading-EdgeSweep on Boundary-Layer Transition at SupersonicSpeeds. NASA TN D-1075, September 1961.
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9. Hanks, G. W.; et al.: F-Ill Natural Laminar FlowGlove Flight Test Data Analysis and Bounday LayerStability Analysis. NASA CR 166051,January 1984.
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11. Banner, Richard D.; McTigue, John G.; andPetty, Gilbert Jr.: Bounda y-Layer-TransitionMeasurements in Full-scale Flight. NASA RMH58E28, Ju ly 28,1958.
12. Jullie, Don W.; and Hopkins, Edward J.: Effectsof Mach Number, Leading-Edge Bluntness, and Sweepon Bounda y-L aye r Transition on a Flat Plate. NA SATND-1071, Sep tembe r 1961.
13. Harvey, W. Don; and Foreman, Brent.: FutureRegional Aircraft Market Constraints, and TechnologyStimuli. NA SA 'I'M 107669,1992.
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16. Boeing Com mer cial Airplanes: High-speed Civil
Transports. NAS A CR 4233, Se ptemb er 1989.
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19. Tice, Dav id C.; and M artin, Glenn L.: A Study ofAltit ude-Constrained Supersonic Cruise TransportConcepts. AIAA 92-1027, Febru ary 1992.
20. Martin, Glenn L.; Tice, David C.; Marcum, DonC.; an d S eidel, Jona tha n A.: A Comparison of Arrow,Trapezoidal, and M Wing Concepts Using A Mach 2Supersonic Transport Miss ion. AIAA 91-3102,September 1991.
21. Seidel, J.; Haller, W.; and Berton, J.: Comparisonof Turbine Bypass and Mixed Flow Turbofan Enginesfor a High-speed Civil Transport. AIA A pa pe r no. 91-3132, September 1991.
22. Carlson, H ~ r r y .; and Darden, Christine M.:Validation of a P air of Com puter Codes for E stimationand Optimization of S ubsonic AerodynamicPerformance of Simple Hinged-Flap Systems for ThinSwept Wings. NASA TP 2828, November 1988.
23. Carlson, Harry W.; Darden, Christine M.; andMann, Michael J.: Validation of a Com puter Code forAnalysis of Subsonic Aerodynam ic Performance ofWings With Flaps in combination With a Canard orHorizontal Tail and an Application to Optimization.NASA TP 2961, Ja nua ry 1990.
24. Harris, Roy V. Jr.: An Analysis and Correlation ofAircraft Wave Drag. NA SA TM X-947,1964.
25. Somm er, Simo n C.; and S hort, Barbara J.: Free-Flight Measurements of Turbulent-Bounday-LayerSkin Friction in the Presence of Severe AerodynamicHeating at Mach Numbers from 2.8 to 7.0. NACA TN3391,1955.
26. USAF Stability and Control DATCOM: Air ForceFlight Dynamics Laboratory, Wright-Patterson AirForce Base, Oh io. rev. 1978.
27. Cam pbell , Brya n A.: Inves tigation of Subsonic
Maneuver Performance of a Supersonic FighterCranked Wing. NA SA TP 2687, July 1987.
28. Ho m, Kam W.; and Ticatch, L. A.: Inves tigationof an Advanced Supersonic Fighter Concept IncludingEffects of Horizontal Tail and Canard C ontrol SurfacesOver a Mach Number Range From 1.6 to 2.5. NASATI' 2526, May 1986.
29. S hrou t, Barret L.: Effect of a Canard and WingLeading-Edge Flaps on the Longitudinal AerodynamicPerformance of a Cranked Wing at Supersonic Speeds.NASA TM 89126, Augu st 1987.
30. McCullers, L. A.: Aircraft ConfigurationOptimization Inc ludin g Optimized Flight Profile. inRecent Experiences in Multidisciplinay Analysis andOptimization, Jaroslow Sobieski, compiler, NASACP 2327, Part 1,1984, p p. 395-412.9.
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0.1 5 5 Mach 5 4.0
40 x l o 6 3 ~ 1 0 ~ ~ ~ , 5 5 2 x 1 0 ~
b 0 NLF flight
0 LFCIHLFC flight
0 NLF wind tunnel
LFCIHLFC wind tunnel
Flag = Shock limited
0 10 20 30 40 50 60 70 80
Leading edge sweep, deg
Figure 1. Effect of leading-edge sweep on transition for wind-tunnel and flight experiments.
Cruise: Mach 2.0
Range 5500 n. mi.
Passengers: 248
Length 295 ft.
Span: 144 ft.
AR: 2.8
Figure 2. 70" - 45" baseline cranked arrow-wing.
Cruise: Mach 2.0
Range 5500 n. mi.
Passengers: 248
Length 295 ft.
Span: 127 ft.
AR: 3.0
Figure 3. 70" - 20" natural laminar flow supersonic transport concept, Rt, 20 x l o6 .
544
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Wing cross-section Fuselage cross-section
70"- 20" 70"- 20" i Arrow-wingconfiguration i configuration
Figure 4. Comparison of fuselage cross-sections
with wing root tank modifications.
Figure 5. Optimized arrow-wing and 70"-20"
configurations, Rtr 20x l o6 .
Figure 6. Estimated natural laminar flow wetted area.
Figure 7. Oil flow on a 70"- 20" fighter configuration
at a Mach number of 1.80.
LID 7.5
5.0
0 70"-20" A2/AT = 0.30
A 70"-20" A2/AT= 0.40
Take-off condition
Figure 8. Effect of wing area ratio (A2/AT) on take-off
performance of 70"- 20" configurations.
0 .5 1O 1.5 2.0
Mach number
Figure 9. Effect of wing area ratio (A2/AT) on
wave drag of 70"- 20" configurations.
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10.0
7.5
LID 5.0
2.5
i0
Figure 10. Wing area ratio (ASIAT) effects on
Mach 2.0 performance,R = 0.
10.0
7.5
LI D 5.0
2.5
i0
10.0
7.5
LID 5.0
2.5
0
Figure13. Wing area ratio (ASIAT) effect on
Mach 2.0 performance,R = 30 x lo6.
\0" 20"configurations
Figure 1 1 . Wing area ratio (APIAT) effects on
Mach 2.0 performance,R = 10x lo6.
Figure 12. Wing area ratio (ASIAT) effects on
Mach 2.0 performance,R = 20 x lo6.
Figure 14. Wing weight effects as a function
of wing area ratio (A2/AT).
looOO1 \7 7 0 0 200configurations
8000
Figure 15. Wing area (S,) variation with
area ratio (A2/AT).
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: :8 Y 7 O e - 2 0 0onfigurations F N ~ ~ f ~ 2 0 x= 0
w -6
.15
W~~
WGTO
Figure 17. Effect of wing area ratio (APIAT)onFigure 16. Wing weight (Ww/WwA) variation take-off thrust-to-weight for turbulent
with area ratio (A,/A~). and R = 20 x 1o6 cases.
0 ayload
OEW1 o Reserve fuel
Block fuel.8
TOGW .6
TOGWA
.4
.2
n
Aircraft
Figure 18. Take-off gross weight comparisons, Rt, = 0. Percent reduction from arrow-wing noted.
0 ayload
OEW1 o Reserve fuel
Block fuel.8
TOGW m6
TOGWA
.4
.2
n
Aircraft
Figure 19. Take-off gross weight comparisons, Rtr= l o x o6. Percent reduction from arrow-wing noted.
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0 ayload
OEW
1O Reserve fuel
Block fuel.8
TOGW .6
TOGWA
.4
.2
n
Aircraft
Figure 20. Take-off gross weight comparisons, R 20x l o6 . Percent reduction from arrow-wing noted.
0 ayload
OEW
Reserve fuel
Block fuel.8
TOGW m6
TOGWA
.4
.2
n
Aircraft
Figure 21. Take-off gross weight comparisons, R = 30 x 106. Percent reduction from arrow-wing noted.
Figure 22. Summary of take-off gross weight variation with area ratio (APIAT)
and transition Reynolds number (R,,).
R = 0
TOGW
TOGWA
.90
.85
/ R t r = 2 0 ~ 1 0 6- A /R , ,=30x l0~-