AN EXPERIMENTAL LEAK TEST FACILITY FOR SUBCOOLED …. Mech...structures such as pipe whip...
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AN EXPERIMENTAL LEAK TEST FACILITY FOR SUBCOOLED WA TER LEAKAGES
S GHOSH1 & S. K. SAHA2 1Department of Mechanical Engineering, Future Institute of Engineering & Management, Sonarpur, Kolkata,
West Bengal, India 2Department of Mechanical Engineering, Jadavpur University, Kolkata, West Bengal, India
ABSTRACT
This paper demonstrates the detail of an experimental leak test facility to simulate loss of coolant accident
(LOCA) probabilities in primary heat transport pipelines of modern pressurized water reactors (PWRs). The facility was
erected at Jadavpur University, Kolkata in collaboration with BARC, Mumbai under a project for reactor safety issues
funded by BRNS, DAE, Govt of India. Unknown crack morphologies concerned were avoided by selecting artificially
generated circumferential slits with rectangular projections on reactor grade Pipelines. Experiments were conducted in
several phases with pressurized (maximum 90 bar) and hot (maximum 250ºc) subcooled liquid water to leak through the
narrow slits on pipe wall oriented perpendicular to pipe flow direction. A bank of Leak flow data has been generated in a
high depressurization flow domain (like 90 bar to atmospheric) and results have been compared with relevant code
predictions, as a function of slit upstream stagnation pressure, stagnation subcooling and slit dimensions.
Thermal hydraulic behavior study of two phase critical flow from narrow slits and concerned code validation demanded a
lot of instrumentation and safety arrangements to achieve proper control over thermal inertia of the huge setup.
KEYWORDS: LOCA, PWR, Sub Cooling, Critical Flow, Leak Test, LBB
INTRODUCTION
Numerous recent pipeline rupture accidents in the oil and gas industries have enforced subsequent stricter safety
design regulations. Interest in the modeling of accidents involving failure of pressurized pipelines started as a result of
research carried out in the nuclear power industry evaluating the critical scenarios of loss of coolant accidents (LOCAs) in
Pressurized Water Reactors (PWRs). The application of Leak before Break (LBB) is for the elimination of protective
structures such as pipe whip restraints, jet impingement shields, etc, which provide protection against high energy line
breaks. LBB methodology has been successfully applied in a number of nuclear power plants. Specially, pressurized water
reactors (PWRs) have been designed to cope up with a catastrophic break on any line for many years. For the Indian
pressurized heavy water reactors (PHWR’s), normal operating conditions are of high pressure (70–100 bars) and high
temperature (260-300ºC). The experimental facilities need to be operated at similar potentially hazardous conditions which
necessitate a robust design backed by detailed analysis. LBB methodology demonstrates that a postulated through wall
crack will ensure a detectable leakage and the flaw will be stable under the severe-most loading with a consequent loss of
pressure. With a capacity of easy detecting a least of mass flow rate 0.05 kg/sec, if 0.5 kg/sec of leak can be shown stable
under the maximum credible loadings, it can eliminate costly shields for postulated rupture and save labor cost,
radiation dosage for normal maintenance and inspection. Real time experiments are necessary to be carried out to estimate
leakage mass flow rate from several stagnation pressure & temperature, slit materials and slit geometries.
International Journal of Mechanical and Production Engineering Research and Development (IJMPERD) ISSN(P): 2249-6890; ISSN(E): 2249-8001 Vol. 4, Issue 5, Oct 2014, 1-12 © TJPRC Pvt. Ltd.
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PREVIOUS WORKS
Simoneau (1974) reported two-phase choked flow rate and pressure distribution data for subcooled nitrogen
flowing through a slit. The slit was a narrow rectangular passage of equal length and width (L/DH=43.5). The results
suggested a uniform two-phase flow pattern with vaporization occurring at or near the exit in most cases. Similar results
can be obtained following the theory of Henry (1970, 1979) for non-equilibrium subcooled two-phase choked flow in long
tubes. Some researchers have studied choked flow through narrow parallel-plate channels. As the boundary layer thickness
formed on the plate becomes zero at the outlet of the channel, it appears as a wall of a converging-diverging nozzle,
resulting in the flow to become supersonic at channel outlet. Taguchi et al. (1996) conducted experiments and a 1D
approximate analysis based on boundary layer equations for the low-density gas choked flow through a parallel-plate
channel, with a narrow gap in the regimes from continuum flow to slip flow. Shi et al. and Miyamoto et al. (2001) clarified
the characteristics of the choked flow in the parallel-plate channel with adiabatic and uniformly heated walls through
experiments. Celata et al. (1988) performed experiments at stagnation pressures of 0.5, 1.0, 1.5 MPa and inlet subcoolings
of 0, 20, 40, 60 degrees to study the influence of a non-condensable gas on a steam-water two-phase critical. Chang et al.
(2002) also performed a series of two-phase critical flow tests at high pressure with a non-condensable gas by using a test
section with an inner diameter of 20.0 mm and a length of 300 mm. As the degree of subcooling (Tsub) strongly affects in
the determination of critical flow rate (Gc), it is necessary to establish the relationship between two parameters
(i.e, Tsub versus Gc). However, the range of subcooling covered in the previous experiments is not sufficiently large
(i.e, less than 30˚C) to quantify the effect of subcooling on the critical flow phenomena. Quantification of the relationship
between Tsub and Gc may help developing a simple critical flow model. In addition, experimental data for small diameters
with real time pipe slits are extremely rare. Present experiments endeavor to seek a longer range of variation in subcooling
as well as stagnation pressure.
SET UP DESIGN
As mentioned earlier, the set up aims to investigate leak flow behavior in predefined domain of stagnation
properties (70 to 90 bar pressure with maximum temperature upto 250 ºC. Transient Thermal- hydraulic analysis has been
carried out in the leak test facility for an open loop system. The facility can be operated by either batch mode or by
continuous mode. The experimental loop was thoroughly investigated including the possibility of pressure surge upstream
or downstream of the slit. Thorough observation provides three sections of the setup identified, namely (i) Primary system,
(ii) Secondary system, (iii) Tertiary system.
Figure 1: Leak Test Facility
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Primary System
Firstly water at atmospheric pressure and temperature is taken from hot well or sump and is stored in an overhead
tank after treatment. In order to avoid corrosion in carbon steel parts in PHT loop, PH of water is kept within 9.8 to 10.3
and the conductivity within 20 to 30 micro-mho The same is achieved by incorporating a water treatment plant
(WTP, Figure 2). An Overhead Tank (OT) stores treated water for batch mode operation. One centrifugal pump is used to
suck the water from sump and send it to the OT through WTP. In WTP, Iron removing filter and Water Softener deliver the
water with following specification: iron < 0.2 ppm as Fe and Hardness < 5ppm as CaCO3. A reciprocating pump (P2) is
used here to force the water to BC from OT. This is low pressure and low temperature loop where pressure is maximum 2
bar and temperature is maximum 45ºC i.e. ambient temperature. Pipe work is mainly done by 40 NB poly vinyl chloride
(PVC) / GI (galvanized iron) pipes. From OT to inlet of P2 pipe is made of 40 schedule mild steel.
Figure 2: Water Treatment Plant
The next phase is high temperature high pressure loop which starts when treated water in buffer chamber sent by
P2 from OT is pressurized by nitrogen gas as topping fluid and then is heated externally by hot thermic fluid.
Buffer Chamber is a very important part of the facility having its capacity of 1250 litre or 1.25 m3. It actually acts as a heat
exchanger (Figure 3). There is a cylindrical shell and two dished ends at the top and bottom of the cylindrical shell.
There is a jacket around the cylindrical shell and insulation around the jacket. The jacket has helical baffle inside to pass
through a hot thermic fluid Therminol 59 which ultimately heats up the water in BC. When the pressure and temperature of
water in BC reach the desired values, then water is allowed to flow through the test section via mass flow meter.
Maximum pressure and temperature of water in HPHT is 90 bars and 250ºc respectively. Buffer Chamber (BC) with
nitrogen gas as topping fluid takes care of the possible pressure surge during the flow of high pressure and high
temperature compressed liquid water through slit in pipe.
Test section is another important part (Figure 4) which contains a cracked test pipe inside housing. The housing
has a rectangular shape with hemi cylindrical part on top. The curvature of the hemi cylindrical portion is designed on the
basis of some experimental data that will prevent the possible jet impingement of steam from the pipe slit. The rectangular
portion is rested on four legs. Test pipe of different diameters are kept on two supports specially designed.
Suitable packing is there for making the arrangement airtight. Two temperature elements (TE: 2A and TE: 2B) are wall
mounted on the test pipe to know the temperature of water inside. One pressure transmitter (PT: 3) is attached to know the
pressure in the housing. This pressure is necessarily the outlet pressure of the leak to be considered for future analysis.
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Figure 3: Buffer Chamber (Top Half) Figure 4: Test Section
Water from either side will enter into the test pipe to produce a pseudo stagnation point in the pipe just before
flow through slit. One 100 mm NB pipeline from the bottom of test section goes to hot well to drain any accumulated
steam and water from test section. Another line from the top of test section goes to a vent tank containing water and a 30
feet high standpipe. This stops any building up of pressure in test section beyond 1 bar. All high pressure and high
temperature pipelines are made of stainless steel (SS316). High pressure (not high temperature) pipe line as well as high
temperature (not high pressure) pipeline is made of mild steel. Pipelines from out let of P2 to BC, from bottom of BC to
hot well and from bottom of BC to test section is made of 20 NB schedule 40 SS316. Pipeline from test section to hot well
is mad of 100 NB schedule 20 MS pipe.
The most important instrument of the whole facility was the flow meter whose working was crucial. A coriolis
type mass flow meter (Figure 5) was attached just upstream to the test section in order to ascertain the perfect measurement
of leak through slits. The specialty of this flow meter is that, it was able to measure the velocity of flow along with flow
rate in liters/min. This velocity can be taken as the inlet velocity for a subcooled flow to be subjected to huge
depressurization rate while coming out from the slits to atmospheric co-ordinates. This data is very beneficial for CFD
analysis of the aforementioned phenomenon with respect to cavitation flashing flow. The mass flow of a u-shaped Coriolis
flow meter is given as , where Ku is the temperature dependent stiffness of the tube, K a shape-dependent
factor, d the width, τ the time lag, ω the vibration frequency and Iu the inertia of the tube. As the inertia of the tube depend
on its contents, knowledge of the fluid density is needed for the calculation of an accurate mass flow rate everything is
done by the meter itself and one needs to bother only about the digital outputs.
Figure 5: A Coriolis Type Mass Flow Meter, Working Principle, Standard Output Device
Secondary System
It is the source of pressurization of the experimental facility (Figure 6). The infrastructure is built up in a separate
room called nitrogen room from the point of view of safety. Nitrogen gas is stored in a bank of 48 cylinders at a pressure of
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130 bars. 24 cylinders are connected to one manifold and the rest 24 are connected to another manifold. A coil shaped Tail
pipe made of copper actually connects a cylinder to manifold with bull noses on the two ends. Two such manifolds are
connected to a single pipe called the main manifold through globe valves GLVN1 and GLVN2. Pipe work is mainly 12.7
mm internal diameter 16 SWG (standard wire gauge) seamless copper pipes for flow of nitrogen at ambient temperature.
But in the pipe line from PCVN to BC there is a possibility of high temperature due to conduction heat transfer. So this line
is made of 20 NB 80 schedule MS pipes.
Figure 6: Secondary System
Tertiary System
It is the source of heat addition of the experimental facility including the following parts. Thermic fluid heater
(TFH) is the main component of heating system which consists of a double start helical coil, burner, fuel pump,
photoelectric sensor, and FD fan. Burner takes the air and high-speed diesel fuel as mixture. Flame is generated with the
help of burner electrode and flame is sensed by photoelectric sensor. Thermic fluid is circulated through the helical coil.
FD fan is there to force fresh air in the TFH and help the flue gases to exit from TFH through chimney. It is located in the
machine room. Actually thermic fluid expands 7 liters per 100 liters of oil per 100ºC rise in temperature.
Deaerator / Expansion tank actually comes into the picture owing to the above consideration. It is placed just outside the
room of test section. A Diesel tank (HSD) is used to store HSD. It is placed just outside the machine room. A Thermic
fluid circulating pump helps to circulate the TF in the experimental facility. It is placed in the machine room. A chimney is
located outside the machine room. It helps flue gases to exit at a high altitude to reduce pollution. High temperature
pipeline is made of mild steel. 76.2 mm (3inch) NB ERW (Electric Resistance Wieldable) pipes are used for the purpose.
Study of the Control Panel
The Control panel is the beauty of instrumentation (Figure 7). It actually builds up the controls of different
instruments used in the experimental facility. It has been incorporated in the experimental facility to bring the complexities
under control. Any kind of irregularities can be noticed by suitable alarms and actions are taken either by automatically or
mechanically through control panel. Most of the alarms and interlocks are routed through a CPU board. In a separate room
called control room this control panel has been placed. Two CCTVs with eight cameras including one rotating camera, two
quad processors and one tilt controller are there. Three phase indications, phase reversal indications, different starter ON,
OFF, trip indications, Firing indications and wrong phase sequence indications are there in the control panel. Temperature
indicating controller (TIC): There are 4 TIC’s in all on the control panel. Three are for the Thermic Fluid Heater and one is
for the Overhead Tank. There are two alarm annunciators in the control panel with 8 channels each. When some fault
appears in the experimental facility, corresponding alarm gets on. If somebody accepts the alarm by pushing the switch
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hooting and blinking will be stopped but the light will be on unless the fault is removed. A microprocessor based
programmable Scanner makes the basis of the Data Acquisitions system. All recorded Data are shown in its display.
The scanner is connected to a computer for storage and data processing was done by software called SERCAP, able to
record 3data every second per channel.
Figure 7: Control Panel
GENERATIONS OF SLITS
Slit generation was by far the most critical section of experimental arrangements. The validity as well as
feasibility of the experimental results is strongly dependent on the accuracy of slit dimensions produced. Reminding the
test matrix slits to be produced was very narrow in the range of less than a millimeter. In this context Amos and Schrock's
(1983) report on critical discharge through slits for USNRC, reminds the use of a U shaped block along with an insert
block and spacer block to create a rectangular opening of particular slit width in the range of 0.13mm to 0.38mm.
However, the present experimental setup was intended to test a real time annular through wall opening which will have a
rectangular projection. It was difficult as well as intricate production work subjected with minute slot dimensions.
To create through wall narrow slits at any circumferential location of pipe wall precision advanced machining was
mandatory. In this case an Electric Discharge Machining was selected to create the minute slots in a rectangular fashion.
The specialty of the machine was the use of a wire as the electrode i.e. a Wire EDM. The whole situation can be
conceptualized by the 3D modeling done using CAD (Figure 8)
Figure 8: Wire EDM Slit Cutting Process on a Round Pipe
As per predetermined test matrix, slits were cut on the pipes. A Wire Electro Discharge Machine was used to
prepare the slits on Seamless 4” NB SS-304L pipes. 3 slits were cut with Slit Width (SW) 0.25mm, 0.38mm, 0.67mm
respectively. Slits were circumferential with an inside & outside arc length of 4.373 mm and 7.75 mm respectively.
Slits can be considered as having a rectangular Slit Opening Area (SOA) on the basis of average arc length 6.178mm and
respective slit widths. Due to the minimum wire size available was 0.25mm, the first slit has undergone some over burn
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with respect to the tolerance and the slit width achieved was 0.268mm.
Figure 9: Standard Operating Procedure
EXPERIMENTATION
On the next phase experiments were carried out for a set of inlet pressure and temperatures. Due to complexities
at different zones of the setup the whole experimental operation was transformed into a series of simpler steps called as a
Standard Operating Procedure (SOP) shown in Figure 9. Transient flow behavior at a good range of subcooling with a
maximum pressure of 90 Bar was thoroughly studied. To ensure safe operation a bank of safety arrangements were
incorporated into the system design and programmed into several instrumentation modules. The whole data acquisition
system included 16 channels associated with several important Transducers, valves and controllers at variety of locations.
RESULTS AND DISCUSSIONS
To attain a steady state condition was a bare necessity to show a stable leakage flow for considerable period of
time. Therefore pressure and temperature of flow was maintained by proper control of the setup during any test run.
For carbon steel pipe slits critical flow was found on development in both cold and hot runs. A code validation program
showed conformity between experimental data and thermal hydraulic code C-SFA (B Ghosh et al, 2004) prediction.
However the code under-predicted the flow rate on an average 20% (figure 10).
Figure 10: Experimental Code Validation SOA=0.057cm2, SW=.038cm, SD=0.8cm
The aforementioned code estimates the pressure drop by calculating the several different forms of pressure drops
experienced by the sub cooled water in the leakage path. The location of flashing inception was assumed as prescribed by
Henry et al. (1970) for homogenous equilibrium flow approximations. More options of the code predicted leak flow on the
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basis of homogeneous frozen flow concept with zero vaporization within the domain. Here, the primary parameter of
material dependence is the friction of depressurizing jet with the slit channel wall. However, the high depressurization rate
and phasic acceleration makes the transit time so small that flow has got the least chance to be majorly affected by pipe
wall friction. And the fact is prominent from the figure 11 where a subsonic unchoked release shows a potential liquid core
region affirming single phase flow within the leakage path. Thus the flow might be governed by single phase pressure drop
terms. A certain degree of superheat due to instant decrease of pressure delays the flashing process resulting in the core
liquid zone.
The unsteady expansion waves in the form of shock dominates the flow when pressure difference is more tending
to a critical choked release involving more unknown parameters in a compressible field. In most cases researchers have
found the flashing to happen at the exit zone or later in case of several L/D ratio ducts and orifices. Therefore a proper
choice of friction characteristics (especially friction factor), governs the code compatibility with practical observations with
smooth or rough slits. Chang K. S. (1999) has discussed about friction factor selection and their dominance while Ghosh B.
et al. (2002) have also enlightened this field.
Figure 11: The Choked and Unchoked Accidental Release Showing a Potential Liquid Core in Both Cases While Unsteady Expansion Waves Governing the Sonic Choked Flow
Present work exploits a study of thermal hydraulic parameters showing their interdependence quite clearly.
Figure 11 and Figure 12 shows a comparative judgment between MS and SS pipe slits of almost similar opening
dimensions. At 80 bar stagnation pressure maintained in the Buffer chamber, the slit flow rate was found to increase with
increasing sub cooling values in both of the cases.
Higher degree of subcooling was achieved at higher pressure keeping the temperature around 240 ºC. Certainly it
increased more delay in flashing and single liquid phase dominance resulting in higher flow rate. Here the analytical code
over predicted when the flow was analyzed on a fixed pressure perspective (Figure 12 a) while the same was under
pedicted in few other observations made on a constant subcooling basis (Figure 12 b).
The mild steel pipes results were affected by high corrosion levels and increased friction. So better conclusions
can be made following the results of stainless steel pipe slits (Figure 13). The basic trend of data continues to be similar in
both of the analysis made at constant subcooling and constant stagnation pressure. The mass flux increases for increased
pressures.
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(a) Variation of Leak Flow with Change in Sub Cooling at 80 Bar
(b) Flow Behavior at 60 Degree Sub Cooling
Figure 12: Flow Behaviors at Constant Pressure and Sub Cooling for MS Pipe Slit, SOA 0.057cm2
(a) Variation of Flow with Sub Cooling at 80 Bar
(b) Flow Behavior at 57 Degree Sub Cooling
Figure 13: Flow Behaviors at Constant Pressure and Sub Cooling for Several SS Pipe Slits
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More results with 4th, 5th slit with increasing slit sizes and slit opening area (COA) have been depicted in
Figure 14 to show the C_SFA code validation exercise. Analysis is stressed here on a fixed subcooling basis and the code
prediction conform the experimental trends. However, a 10 to 20% under prediction was found in all cases as shown in the
overall plot (Figure 10) too.
(a) Variation of Flow with Pressure at 67 ˚C Sub Cooling with COA 5.91×10-6 m2
(b) Variation of Flow with Pressure at 39 ˚C Sub Cooling with COA 8.05×10-6 m2
Figure 14: C-SFA Code Prediction Compared to Experimental Observations
CONCLUSIONS
The experiments done with narrow slits of varied dimensions involved a lot of thermal intertia to be handeled.
However the error analysis provided an associated uncertainity with leak flow rate are varying between 0.186% and
_1.98% of the estimated value with 95% level of confidence which is quite satisfactory. The C_SFA code validation study
indicated the physical correctness of the experimental results. Moreover the success of a perfect code prediction lied in the
selection of friction factor selection and the use of a suitable discharge coefficient. Although the discharge coeffiecients
were set 1.0 for most cases in this study, a suitable value can be ascertained from the comparative plots. Analysis were also
made on the basis of L/D ratio changes with varying slit dimensions. However most of the data trends conformed the
results found by Amos & Shrock (1983, 1984). Repeatability tests were done on few slits to confirm the present trends and
behavior with satisfactory affirmations. As a whole stable leakage at around 0.5 kg/s through narrow slits resulting into a
flashing two phase exit flow at nearby critical flow velocities was confirmed. Such leakage can be sensed well by modern
instrumentations and sorted down without hampering useful production time at lower costs.
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ACKNOWLEDGEMENTS
The author is thankful to the Board of Research in Nuclear Sciences, Department of Atomic Energy, and Govt. of
India for financing such project of experimental code validation which opened up many uncertains domains of critical
flashing flow through high pressure pipeline leakages. Many thanks to Mechanical Engg. & Production Engg. Department
of Jadavpur Univeristy for housing such project giving chance to explore new domains of fluid flow and plant safety.
Sincere gratitudes for other investigators and collaborators too.
REFERENCES
1. Abdollahian, D, Healzer, J, Janssen, E, Amos, C,(1982), Marviken data: critical flow data review and analysis.
Electric Power Research Institute, EPRI-NP-2192
2. Amos C. N. and Schrock V. E, (1983), Critical Discharge of Initially Subcooled Water through Slits,
NUREG-CR--3475, USNRC.
3. Amos C. N. and Schrock V. E, (1984), Two-Phase Critical Flow in Slits, Nucl. Sci. Eng, 88, pp.261-274
4. Celata G. P, Cumo M, Annibale D, Farello F, G. E, 1988, The influence of non-condensible gas on two-phase
critical flow. Int. 1. Multiphase Flow pp. 14, 175-187.
5. Chang. K. S, Uncertainty Analysis of Leak Rate Calculation through Pipes and Slits, Annals of Nuclear Energy,
Volume 26, Issue 5, March 1999, Pages 411–422
6. Chang, S. K, Park, H. S, Chung, C.H, (2002) b. Two-phase critical flow with non-condensable gas on sharp-edged
short pipe geometry. In: Proceedings of the Korea Nuclear Spring Meeting, Gwangju, Korea, and May
23-24.
7. Experimental Facility for Validation of Critical Leak Rate Models and Thermal Fatigue Monitoring
System”- Project Number: 2000/36/7/BRNS dated: 27.7.2000- Final project report ,September,2005
8. Ghosh S, Mukhopadhyay D, Ghosh B, Bandyopadhyay S. K, Saha S. K, Misra D, Behera G, Measurement and
analysis of critical leak flow rates through slit using high-pressure high temperature leak flow measurement
facility at Jadavpur University and Code Validation, 19th National & 8th ISHMT-ASME Heat and Mass transfer
Conference, NHT 26, January3-5,2008, JNTU college of Engineering, Hyderabad.
9. Ghosh S, Mukhopadhyay D, Mondal S, Saha S. K, Experimental Investigation of Subcooled Critical Flow
Through Slits, 20th National and 9th International ISHMT-ASME Heat and Mass Transfer Conference, January
4-6, 2010, Mumbai.
10. Giot M, Two-phase releases, Journal of Loss Prevention in the Process Industries Volume 7, Issue 2, 1994, Pages
77–93
11. Henry R. E, 1968. A study of one- and two-phase critical flows at low qualities. ANL-7430, Argonne Natl. Lab.
12. Henry, R. E, 1970. The two phase critical discharge of initially saturated or subcooled liquid. Nucl. Sci. Eng. 41,
336 - 342.
12 S Ghosh & S. K. Saha
Impact Factor (JCC): 5.3403 Index Copernicus Value (ICV): 3.0
13. John H, Reimann J, Westphal F, Friedel L, Critical two-phase flow through rough slits, International Journal of
Multiphase Flow, Volume 14, Issue 2, March–April 1988, Pages 155–174
14. Lee J. B, Young H C, 1999. Application of LBB to high energy pipings of a pressurized water reactor in Korea,
Nucl. Engg. Design. 190, pp. 191-195
15. Measurement of Critical Leak Flow Rates through slit using Leak Flow Measurement Facility at JU and code
Validation-Project Number: 2005/3642/BRNS/2508, dated: 20.2.2006-Final project report, May, 2007.
16. Shi W, Miyamoto M, Katoh Y, and Kurima J, “Choked Flow of Low Density Gas in a Narrow Parallel- Plate
Channel with Adiabatic Walls,” International Journal of Heat and Mass Transfer, Vol. 44, 2001, pp. 2555-2565.
17. Simoneau R. J, Two-phase choked flow of subcooled nitrogen through a slit, Lewis Research Center Cleveland,
Ohio 44135, NASA-TN-X-71516).
18. Rudland D. L, Wilkowski, G. and Scott P, Effects of crack morphology parameters on leak-rate calculations in
LBB evaluations. International Journal of Pressure Vessels and Piping, 79, 2, 99-102, 2002.
19. Sallet D. W, Critical mass flow rates through pressure relief valves, College Park, Maryland, USA, Warme und
Stofffibertragung 26, Springer-Verlag 1991, 315-321
20. Sozzi G. L, and Sutherland W.A, Critical Flow of saturated and subcooled Water at High Pressure,
General Electric Company, NEDO-13418, July, 1975.
21. Taguchi T, Hirai E; Kato M, Miyamoto M, Katoh Y, Nagata T, Discharge Characteristics of Low-Density Gas
Flow through Parallel Plate Channel with Narrow Gap, JSME International Journal Series B; ISSN:1340-8054;
VOL. 39; NO. 3; PAGE. 470-474; (1996)