ML20052G126
| ML20052G126 | |
| Person / Time | |
|---|---|
| Site: | Big Rock Point File:Consumers Energy icon.png |
| Issue date: | 05/10/1982 |
| From: | Prelewicz D CONSUMERS ENERGY CO. (FORMERLY CONSUMERS POWER CO.), NUS CORP. |
| To: | |
| Shared Package | |
| ML20052G119 | List: |
| References | |
| ISSUANCES-OLA, NUDOCS 8205140332 | |
| Download: ML20052G126 (50) | |
Text
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UNITED STATES OF AMERICA NUCLEAR REGULATORY COMMISSION s
BEFORE THE ATOMIC SAFETY AND LICENSING BOARD In the Matter of
)
) Docket No. 50-155-OLA CONSUMERS POWER COMPANY
) (Spent Fuel' Pool
)
Modification)
(Big Rock Point Nuclear Power Plant)
)
TESTIMONY OF DANIEL A. PRELEWICZ CONCERNING THERMAL HYDRAULIC CONDITIONS FOR CRITICALITY ANALYSIS My name is Daniel A.
Prelewicz.: I reside at 6901 Keats Court, Rockville, MD.
Starting June 15, 1978, I was employed by NUS Corporation, an engineering service firm in Gaithersburg, Maryland.
I am currently a Consultant to NUS Corporation, and until recently I was Manager of the Safety Analysis Department at NUS.
Prior to my association with NUS, I was a Senior Engineer in the Thermal and Hydraulics Develop-ment Section at the Westinghouse Bettis Atomic Power Labora -
tory in West Mifflin,' Pennsylvania.
A resume which describes my background and qualifications is attached.
INTRODUCTION In its Order and Memorandum of February 5, 1982, the Licensing Board questioned the adequacy of the criticality analysis prepared for the expansion of the Sig Rock Point 4
0205140332 820510 PDR ADOCK 05000155 T
. spent fuel pool.
Specifically, the Licensing Board adopted the argument advanced by the Intervenors, namely that:
I
[The c]riticality analysis performed by Dr. Kim is based on a water temperature of 212'F, dsSuming boiling of the spent fuel pool, with the containment at atmospheric pressure.
Even assuming that the containment is at atmospheric pressure (not necessarily conservative after a LOCA [ loss-of-coolant acci-dent]), the pressure at the bottom of the spent fuel pool, due to the hydrostatic load is 28.14 psia.
The boiling tem-l perature at that pressure is
'247'F.
Since the effective activity coefficient K is not permitted to exceed 0.95, and since Dr. Kim's calculations reached this maximum, assuming 212*F, it is questionable if the calculations can be considered conservative.
My testimony provides the thermal conditions for use in the criticality analysis.
This testimony describes both the natural circulation cooling process in the Big Rock Point spent fuel pool and the manner in which pool thermal condi-tions are determined.
The case considered is the loss of all pool cooling systems with a subsequent rise in pool water temperature to 212*F, which is the boiling tercerature at the surface of the pool.
i i
4 SATURATION (BOILING) TEMPERATURE OF WATER The properties of water are such that its tempera-3 ture increases until it reaches a certain temperature called its saturation temperature.
The saturation temperature is a well-defined function of pressure with the saturation tem-perature increasing as pressure increases.- The relationship l
between saturation temperature and pressure is given, for example, in the ASME Steam Tables (Reference 1).
j The pressure in the Big Rock Point spent fuel pool will increase with depth due to the hydrostatic head of water in the pool.
Pressure will increase from about 14.7 psia at the surface of the pool to 26.5 psia at the bottom of the pool.*
Saturation temperature will, therefore, increase from 212*F at the surface to 243*F at the bottom of the pool.
Once the saturation temperature is reached, further energy input to i
'the water goes into generation of steam bubbles rather than further increases in temperature.
The temperature / pressure relationships set forth in the ASME Steam Tables determine the boiling point of water.
The pressure of 28.14 psia suggested by the Licensing Board is inconsistent with a water depth of 28.42 feet and water density at 212'F.
Therefore, the saturation 3
temperature at the bottom of the pool is 243'F rather than 247'F.
1 However, in the Big acek Point spent fuel pool, a natural circulation process occurs which prevents the water from reaching the boiling point at many locations in the pool..The saturation temperature is thus the maximum temperature that can be reached at any depth and not necessarily the tempera-ture that will be reached.
NATURAL CIRCULATION COOLING PROCESS In the spent fuel pool, heat generated in the fuel, located near the bottom of the pool, as shown in Figure 1, is transferred to the water.
As the temperature of the water increases, its density decreases and, hence, the water becomes lighter.
A situation in which the temperature increases with depth is therefore unstable, in the sense that the lighter warmer fluid at the bottom will rise to the surface and be replaced by the cooler heavier fluid which will flow downward from the surface.
When heat is continuously added to the water, a natural circulation flow pattern will be established whereby the heated water, driven by buoyancy forces, rises l
continuously to the surface near the center of the pool, while cooler water flows downward near the pool walls, as shown in I
Figure 1.
i t
l
! BIG ROCK POINT SPENT FUEL POOL THERMAL HYDRAULIC CALCULATIONS A conservative calculation of the thermal conditions in the spent fuel pool was performed by me for the case of loss of all pool cooling systems using the computer program i
SFPT2.
The analysis models natural circulation flow in the most limiting location in the pool.
The model is based on one-dimensional flow in the pathway, known as a downcomer, between the pool wall and the racks and up-flow through a row of eleven fuel bundles which are fed by the downcomer.
This type of model is conservative because it neglects flow'to the row of fuel bundles from sources other than a. single downcomer (i.e.,
from downcomers adjacent to the pool walls parallel to i
the row of bundles).
Licensing calculations typically use this form of conservative model.
This steady-state calculation balances the buoyancy forces and flow losses to obtain the flow rates in the down-comer and each fuel bundle.
The inlet temperature of the j
water is taken as 212*F, and the heatup of the water as it rises through the fuel bundles is calculated from an energy i
balance.
All eleven fuel bundles are conservatively assumed to generate an amount of heat equal to that of the most limiting fuel bundle.
(
l l
. The analysis establishes that_the water in the most i
limiting bundle will reach the saturation temperature of 237'F at.276 inches below the top of the bundle.
As I stated earlier, once the saturation temperature _is reached, further energy input to the water goes into generation of steam-bubbles rather than into further increases in temperature. The water temperature in the region from the bottom to the top of the fuel will vary from approximately 212*F at the bottom to 237'F at the top.
Therefore, the average water temperature over the active fuel height is 224.5*F.
At the point in the fuel bundle (.276 inches below the top) where the temperature of the fluid reaches the saturation temperature, bubbles will begin to. form in the bulk fluid.
The length of the bundle over which this occurs is referred to as the boiling length.
The driving force for the natural circulation flow is the density difference between the cooler fluid which is flowing downward near the pool walls and the warmer fluid which is rising in the fuel bundles.
The flow in a given bundle will increase significantly when voids (i.e., bubbles) are formed near the exits of that bundle.
This is due to the low density of the steam voids compared to the high density of the cooler water.
A mechanism is thus provided which tends to equalize the amount of voiding among l
l l
L
. the various bundles.
This limits the extent of the boiling length, which is calculated to be.276 inches.
The extent of void formation in tite boiling length is determined from an energy balance equation.
At the exit of-the bundles, only about.0126% of the fluid mass is converted to steam.
This corresponds to a void fraction (i.e., ratio of steam volume to total fluid volume) of approximately.206 at-the bundle exit.
The void fraction will vary over the boiling length from zero at the start of boiling position to.206 at the exit.
THERMAL CONDITIONS FOR CRITICALITY ANALYSIS Originally Dr. Kim was provided with the information that the thermal conditions in the spent fuel pool were a coolant temperature of 212*F and an exit void fraction of 20.6%.
In view of the concerns expressed in the Licensing Board's Order and Memorandum regarding the thermal conditions used for the criticality analysis, and Dr. Kim's results which show that k-effective increases with increasing coolant temperature, I have provided Dr. Kim with the following, more realistic, thermal conditions.
As described in the preceding section, the fluid condition in the fuel bundles varies along the length of the bundle from approximately 212'F water at the inlet to 237'F
. fluid, which is 20.6% steam by volume, at the exit.
Bulk voids exist only for the upper.276 inches of the channel.
The average temperature over the active fuel length is 224.5'F.
1 DETAILED NATURAL CIRCULATION COOLING CALCULATIONS To verify that the temperature of the water entering the bottom of the fuel racks is approximately 212*F, detailed-calculations of the natural circulation flow patterns in the spent fuel pool were performed with the GFLOW computer pro-gram.
This analysis is attached as Exhibit A.
GFLOW models a representative section of the fuel pool in three dimensions 3
and determines the velocity and temperature throughout the pool.
The computer program solves the governing equations'of conservation of mass, energy, and momentum for each of a large number of cells into which the pool is divided.
An energy -
equation for the spent fuel is also solved to determine the energy input to the water.
Flow in the fuel racks is treated as flow through a porous medium.
The governing equations are solved by a modified " marker and cell" technique.
Results of the analysis demonstrate that natural l
circulation patterns are set up in the fuel pool which cause i
the water entering the bottom of the fuel racks to be approxi-mately equal to 212*F.
This analysis verifies the assumption that water enters the bottom of the fuel racks at 212*F in the 1
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_g_
one-dimensional licensing analysis discussed previously.
The i
temperature of the water in the pool will hence not reach 247' as suggested by the Licensing Board.
POST-LOCA CONTAINMENT OVERPRESSURE The containment pressure assumed for the thermal analysis discussed above was 14.7 psi.
Immediately'following a Loss-of-Coolant Accident ("LOCA"), the pressure in the con-tainment may reach as high as 23 psi above the 14.7 psi value I
as noted in the testimony of Mr. David P. Blanchard, and as l
shown in Figure 2.
As Mr. Blanchard explains, the containment.
pressure returns to near ambient (i.e.,
14.7 psi) within about eight hours after the accident.
Since the minimum time for the spent fuel pool to reach a boiling condition (which is the limiting condition analyzed in the criticality analysis) has been conservatively calculated to be 20 hours2.314815e-4 days <br />0.00556 hours <br />3.306878e-5 weeks <br />7.61e-6 months <br />, the 23 psi overpressure will not occur concurrently with spent fuel pool boiling.
The calculation of the time to reach boiling in the spent fuel pool was discussed in my prior testimony on Spent Fuel Fool Boiling.
Given the time separation between the occurrence of peak containment pressure and fuel pool boiling, it is not necessary or proper to analyze pool boiling at the post-LOCA containment overpressure condition.
[
1 i
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l
REFERENCE:
l l
1.
C. A. Meyer, et al.,
"ASME Steam Tables," American l
Society of MecEaiiTcal Engineers, 3rd Edition, 1977.
l l
\\
DANIEL A. PRELEWICZ EDUCATION California Institute of Technology, Ph.D., Applied Mechanics,1970 State University of N. Y. at Buffalo, M.S., Engineering Science, 1967 State University of N. Y. at Buffalo, B.S., Engineering Science,1965 REGISTRATION Professional Engineer (Mechanical), Pennsylvania,197S SECURITY CLEARANCE DOE - Q EXPERIENCE ENSA, Inc., 1982-Present NUS Corporation, 1978-1982 Westinghouse Electric Corp., 1973-1978 Washington University (St. Louis), 1970-1973 ENSA, Inc. -- As Vice President of Engineering responsible for providing consulting services in the areas of fluid systems, thermal-hydraulics analysis, nuclear safety and irradiations test services. Lead responsi-bility for development and application of the FLOSYS computerized fluid systems analysis methodology.
NUS Corporation -- As Manager of the Safety Analysis Department provided management supervision of activities in thermal-hydraulics and safety analysis including the areas of nuclear plant transient and accident analysis, core thermal analysis, hydrodynamic loading, containment and subcompartment analysis, fluid systems design analysis and thermal design.
Lead thermal analyst on Title I design of upgrade fuel for the TREAT reactor. Developed and conducted a safety analysis training program for utility staff.
Served as consultant on FLECHT-SEASET reflood heat transfer test program.
Developed computer code for analysis of natural circulation cooling of spent-fuel, pools under off-nominal, two phase conditions.
Performed analyses of blocked-bundle steam flow, containment fire effects, spent-fuel pool natural circulation cooling, BWR turbine trip, and HELB outside containment.
Conducted technology surveys on PWR reactor vessel fracture toughness and pressurized thermal shock, BWR core spray effectiveness, and pipe whip effects.
Westinghouse Electric Corp. -- Provided technical lead in the development and qualification of computer programs, including FLASH-6, for accident analysis of nuclear power reactors; provided consultation on the use of computer methods for safety analysis, and analyzed benchmark problems to qualify safety-relt.ted computer codes. Designed and procured a test loop ENSA,inc.
DANIEL A. PRELEWICZ Pfge 2 for hydraalic pressure surge testing related to LOCA and check valve slam structural loadings. Conducted pressure surge tests, including tests on the effects of clastic and plastic coupling.
Performed contain-ment analysis for a heavy water test loop.
Washington University (St. Louis) -- As Assistant Professor of Applied Fbthematics and Computer Science with a joint appointment in the Department of Mechanical Engineering, was Co-investigator on a research project
" Concepts for a Theoretical and Experimental Study of Lifting Rotor Random Loads and Vibrations", funded by the U.S. Army. Methods were developed for identifying parameters of helicopter rotor dynamics models from test data.
MEMBERSHIPS American Society of Mechanical Engineers American Nuclear Society American Institute of Aeronautics and Astronautics Tau Beta Pi Sigma Xi REPRESENTATIVE PUBLICATIONS
" Evaluation of Flow Redistribution Due to Flow Blockage in Rod Bundles Using COBRA Code Simulation" (coauthor), EPRI NP-1662, Project 1380-2 Final Report, January 1981 FLASH -6: A FORTRAN-IV Computer Program for Reactor Plant Loss-of-Coolant Accident Analysis (LWBR Development Program)", (coauthor) ERDA Research and Development Report WAPD-TM-1249, July 1976
" Hydraulic Pressare Pulses with Structural Flexibility: Test and Analysis (LWBR Development Program)", ERDA Research and Development Report WAPD-TM-1227, April 1976. Abstract published in Transactions of the American Nuclear Society, Vol. 24, November 1976, pp. 294-295
" Computer Experiments on Periodic Systems Identification Using Rotor Blade Transient Flapping-Torsion Responses at High Advance Ratio", (coauthor),
Proceedings of the Specialists Meeting on Rotorcraft Dynamics, NASA Ames Research Center, February 13-15, 1974
" Response of Linear Periodically Time Varying Systems to Random Excitation",
AI AA Journal, Vol. 10, No. 8, August 1972, pp. 1124-1125 ENSA,inc.
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FIGURE 1-SPENT FUEL COOLING l
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S O
SPENT FUEL POOL THERMAL-HYDRAULIC ANALYSIS FOR BIG ROCK POINT PLANT O
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CORPORATION DATE kb CLIENT CwMt*WMYCM M FILE NO. 6 OM -
o BY SUBJECT G - F lcm Aut#.stE Checked By Client:
Consumers Power Company Analysis File No.:
5148-SA-A6 O
Analysis
Title:
Spent Fuel Pool Thermal-Hydraulic Analysis for Big Rock Point Plant Author Identification: Dr. Rodney R. Gay 0
Purpose of Analysis:
To predict asing a three-dimensional, conservative analysis (GFLOW Code) the coolant inlet temperature at the bottom of the fuel storage racks when there is zerogoolant flow into and out of the storage pool, and the pool surface temperature is 212 F. Also, the maximum pool water temperature, and fuel surface temperature will be predicted, as well as the flow rates through the heated regions of the pool.
O This analysis is in support of the one-dimensional analysis performed by the SFPT2 code (Reference 1). It is intended to illustrate the natural circulation flow process and to verify the assumption of 212 F coolant temperature below the fuel storage racks.
General Method of Analysis:The GFLOW code (Reference 2) was used to simulate the O
three-dimensional response of a section of symmetry of the Big Rock Point fuel storage pool enclosing the new "F" fuel rack. Conservative valves were used for irreversible pressure loss coefficients in the downcomer and fuel regions. Two regions of the pool containing over 16 fuel assemblies were conservatively assumed to operate at 2.73 (F, maximum peaking factor) times the average assembly heat load. The pool surface tehperature was maintained at approximately 212 F by selecting a convective o
heat transfer coefficient and air temperature which result in the total fuel heat production being convected out of the top of the pool when the pool surface g
temperature is 212 F. Zero coolant flow is pumped into and out of the pool.
Input Information (Reference 1) g Fuel Assembly Parameters Rod outside diameter:
.449 in
.0374 f3 /
=
Assembly flow area:
.163 ft Rods per assembly:
121 No. of spacers 3
5.83 ft /
C Active fuellength:
70 in
=
Fuel assembly power factor 1.45 Axial peaking factor 1.51 Local peaking factor 1.20 Engr. heat flux factor 1.04 Product of above four factors 2.73 O
Storage Rack Floor to top of rack:
8.04 ft From top of rack to fuel:
1.01 ft Depth of top of fuel:
21.38 ft O
Floor to bottom of rack:
0.5 ft
Prg* b 10 of l
CORPORATION DATE 4-13-82 5148-SA-A6 R.
R.
Gay CLIENT FILE NO.
BY SUBJECT C Flow Analysis Checked By,
FLUID PROPERTIES (Reference 4)
O lbm BTU f
59 8086 hf = 180.07 at 212*F
=
ft3 lbm*F 58.82353 hg = 218.48 at 250*F
=
g 59.8086 58.82353 COEFF. OF EXPANSION =
=
(250 - 212)
O
.025923 lbm slugs y
=
.000805
=
3 ft eF ft 'F 218.48 - 180.07 SPECIFIC HEAT
=
0 250 - 212 BTU /
ft - lbf slugs /
1.01 X778 X 32.2
=
lbm*F BTU lbm ft - lbf
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O 25300
=
slug
'F 1
VISCOSITY MU =
0.683 sec X h
ft 3600 ldm ft hr 32.2 lbf sg2 lbf - sec
-6 MU =
5.9 x 10 2
O ft BTU ft - lbf sec 0.395 778 3600 CONDUCTIVITY CONDF
=
hr ft*F BTU hr ft - lbf n
/
.0854 CONDF
=
sec - ft - 'F GRAVITY GC = 32.2
/
seC O
O
-d Paga of
'~)
4-13-82 CORPORATION DME CPCo 5.49-SA-A6 R.
R. Gay CLIENT FILE NO.
BY G Flw Analysis Checked By A
SUBJECT O
FUEL ROD PROPERTIES (Reference 5)
SPECIFIC HEAT OF FUEL:
x
-6
.07622 + 1.16.10
(
T + 255.2) + ( 1 +x)8-CDF
=
0 (6.76x10 / [R (
+ 255.22) 2))
6 x = esp [ 6.25 - 42659/ (R(h + 255.22)))
Where O
r=
1.987 Let T = 250*F:
then 5/9T + 255.22 = 394.11 /
-21 x = ex p (6.25 - 42659/[1.987 (394.11))) = 1.1 x 10 j
-6 x CPF =.07622 + 1.16.10 (394.11)
O
- 1
/ CPF =
.0767 X 778 V 32.2 s ug lbm*F BTU f t lbf CPF =
1921 j
O slug *F SPECIFIC HEAT OF CLAD
-5
.06805 + 2.3872.10
( (T-32) /1. 8 )
=
C,)
-5
.06805 + 2.3872.10 (121)
BTU ft - lbf 1*
.0707 778 32.2 0707 x =
lbm F BTU slug ft l f
, ay, 1776 O
=
slug p
From Graph on p.253 of Reference 5:
Conductivity)
KFUEL =
42 hr-t F BTU hr of Fuel and l O
Clad
(
KFUEL = 0.908 E ~II /
sec ft F
-3 +1.674x10-6 2
-10 3 T
T -3. 334::10 7
KCLAD = 7.151+2.472x10 l*7bec?
/
f KCLAD = 7.869 hr-F f
F g
.o
AO l
4:
Pag? 7 of CORPORATION OATE 4-13-82 CLIENT CPCo FILE NO.__ 5148-SA-A6 sy R.
R. Gav SUBJECT G Flow Analysis Checked By.
GAP HEAT TRANSFER COEFF.
BTU J
Assume H GAP = 1000 (778/3600) 2 hr-ft.7 ft - lbf H GAP = 216 j
sec - ft
'F 3
DENSITY OF FUEL lbm f RHOF =
(75% theoretical density) x 32 h
su RHOF = 20.2
_ t e
DENSITY OF CLAD
/
RHOC=410d.*[32.2 I
slu s /
RHOC = 12.7 ft 0
0 Pool Dimensions 28.416 ft (Reference 1)
Depth:
=
Width:
239 in /
19.92 ft (Reference 3) /
=
25.94 ft (Reference 3) /
Length:
311.25 in /
=
9 9
Pg of AO 3
4-13-82 OATE CORPORATION 5148-SA-A6 R. R.
Gay CLIENT CPCo FILE NO.
BY G Flow Analysis Checked By SUeJECT J-VOLUMETRIC HEAT GENERATION RATE (Reference 1) bf/3600 4 BTU ft -
Assembly Heat Output = 4.1x10 y 77g
']
ft-lbf /
Q = 8860.5 sec 0
ft-lbf
/
73.23 Heat Generated per Rod =
=
(11) (11) sec O
ft - lbf Volumetric Generation Rate =
see T (.0166 f t) 5.83ft ft - lbf 3., go 7 g
= 14502 eei sec ft3 g
SURFACE AREA OF POOL PER FUEL ASSEMBLY
~
b Width of "F" Rack Assembly =
Number of Risers
,i 3
/
2 1
73.25 in.
A ssembly =
A 12 h (8 risers)_
2 C
Assembly = 0.582 ft
/
POROSITY OF RODDED REGIONS Assembly Flow Area A Assembly g
2
.163 ft 4,
.582 ft
/
& Assembly = 0.28 O
O O
^O 4NUS i
Prc,
- cf 3
^
O ~*~,
CORPORATION OATE FILE NO. 9 U S ~ S ~~
BY S E CAM C
CLIENT b IW ANM Checked By P
SUBJECT Major Assumptions:
1.
Constant density water in pool.
2.
Bouyancy force is equal to a constant times fluid temperature.
3.
Response of whole pool can be modeled by simulating a region of the pool only as wide as the "F" rack.
)
4.
The top surface of the pool is held at approximately 212 F by heat transfer (no masstransfer) which equals thg fuel heat generation rate when the top surface temperature of the poolis 212 F.
5.
Entire fuel region is assumed to be of identical geometry and heat generation rate except for specified nodes which are at 2.73 times the power of the other 3
fuel assemblies.
This assumption results in conservatively high total power production, but does not model the actual power distribution.
6.
Fuel region can be modeled as a porous medium.
7.
Constant specific heat and thermal conductivity are assumed for all pool 6
materials.
8.
Radial temperature distribution in fuel (UO ) is assumed to be parabolic.
2 9.
Zero shear stress in f!uid (slip boundary condition) is assumed on front surface of the pool region modeled by GFLOW.
O e
important References 1.
D. A. Prelewicz, " Spent Fuel Pool Thermal-Hydraulic Analysis for Big Rock Point Plant," NUS Analysis File No. 5148-SA-A2 (10/26/78), Supplement 1 (11/3/78), Supplement 2 (12/28/78) and Supplement 3 (6/8/79). Status: Final g
2.
R. R. Gay, " Gravity Driven Flow and Heat Transfer in a Spent Nuclear Fuel Storage Pool," NUS Corporation Report NUS-3916, October 1981 (proprietary).
Status: Final D
0
I 10 j
1 Paga of pg
! i Q@OMON DATE 9-O ~
FILE NO. b U-SA~ N BY b O bA CLIENT C
b EW WWD5 O
SUBJECT Checked By,
3.
NUS Drawing No. 5148M2000, Rev. E. Status: Final O
4.
C. A. Meyer, et. al., "ASME Steam Tables," American Society of Mechanical Engineers,4th Ed.,1979. Status: Final 5.
R. J. Lahey and F. J. Moody, "The Thermal-Hydraulics of a Boiling Water Nuclear Reactor," American Nuclear Society,1977. Status: Final O
Identification of Computer Codes and Computer Used The GFLOW (Reference 2) NUS proprietary computer code was used for this analysis.
GFLOW analyzes a three-dimendional rectangular porous medium by dividing up the porous medium into a number of nodes or cells specified by the user. The finite difference form of the fluid conservation equations is solved for each node by L>
application of a modified " marker and cell" numerical technique. The existence of spent nuclear fuel in any node is modeled by inputting a porosity value less than unity in that node and by including a surface heat transfer term in the fluid energy equation.
In addition, local pressure losses due to grid spacers or other planar flow obstructions may be modeled by local loss coefficients. Heat conduction in the fuel i= simulated by a fast running implicit, finite difference model of the fuel, gap and cladding regions of O
the fuel rod.
The calculations were performed on the University Computing Company Cyber 176 computer (NOS/BE System) at Dallas, Texas.
GFLOW calculations have been performed for another fuel pool and compared to calculations of another code in Reference 2. The GFLOW computer code is presently an unverified code O
and it's status is therefore experimental.
'O O
.O o
i
+NUS o'
l CORPORATION DATE N - I3' 0--
CLIENT O
FILE NO. 6 N 9 b' 'S BY UN b - E'M AM'D '-
Checked By E'
SUBJECT 7ET Au_G C C.gg_. wpm oW Poet.
C-G.o MET GLM To e vig.va C PE,N C
SPACC-
~
/
f)ow'dCc"fR/
O K
'Y 7 b.- - - - - i. _ '- - -i_/_ _/ /_.1_. / _ a. t / /
N---
7 i
.--~
Q, a_,j
,/__ /_ '
/-
T--~~
179' i
1
/
// ///,
, '.'. / /_/ a' -
n
, _i_ _./_ i;
/
. _/,' /
s.,o il__ _L.v,'.'.._/ {- [_i _'. /.1,l. Uj _ _
li s t i, ' ^
,.\\-c.fr
//y /
l ll / _/
i a
i iL
_4
+
l,.! )'fi/
ll /j'l -)t._ - - _. %'// s//
j i/
,.s.2 v '
w _ _/_',.l,//.i
,/
3
._ c-
. f,lj',,{' !,' ','
/jl,4
',!! I 'f/ ' /,{l I
/
2 y 2
3 y
s c
e r
Dowwtown. wea.ce_Ted m ms sics.
O Poot.
G E o w E v a_9 dos. y sqw l' ?)
-'t,g
- A I
+
4.20'
$,Z l '_-y- \\ t 9 ' y 4.2 8 'm 1.2 8 ' u
-pe-4.2.1 l
f l
1 I
l I
O 7
l l
5'. 5** '
I I
l l
gl
.t_ __ _ _4 _
__ _4 4_
l i
l l
l r.sfc '
I i
lO
.L_
_ _g _ _L _ _ __
_g__
__________y i
l
~
i i
7 rm s."
I l
I i
I l
_.L _ _ _ _ _ _ _ _ _ _ _._ _
_L -
_y-0 l
l 4
I l
l S. if 5' i
i I
5
. l' f!Y I
!'!f/!l'/,h.,.}--
'/
W
, __ i _;./w w ' --- &
7n
/ /
7i o
y
///
3
/'
/
d '
l,
/
o.c '
/-
g--
a
_ l l
T I
,. o '
v i
r T
mmou }
ovee
%cu
.O
UNUS
~
~
N~13-E CORPORATION DATE CLIENT Co FILE NO. b M-N'S BY SUBJECT C ELOW MACO\\h I'
'O Checked By Pool Geometry Modeled GFLOW was used to model only the "B" and "F" racks and the adjacent downcomers as O
shown below. Dimensions of the GFLOW model are:
X Direction: Length is that of BRP pool.
Y Direction: Full depth of BRP pool is modeled g
Z Direction: Dimension equals width of "F" rack plus downcomer
=
74.25"+3.5" = 76.75 inches /
Downcomer thickness of.584 ft. Is twice the actual thickness, to improve GFLOW nume:ics. In the fuel region the porosity of the downcomer is set equal to 0.5 to give j
correct flow area. Downcomer on left hand side of fuel region was neglected, a o
conservative assumption which makes modeling easier.
Open space region simulates actual open region in the BRP pool.
Top View of Entire Pool O
MT Ntso S-o f
y} '
/
,y' d,
b G%w moogt is g
t
\\
7,> N
'2),
77* CF W: SHAc60 y
c V-
'\\
\\,
- Eh o
~4 *Je_
,A,,
pm W.O*
hk A
~
a' Mo:
's m
,, p, o
JL b
10.2f
M O
O
'**L !
+
o DATE
.s -
QRPORATION CLIENT C
FILE NO. Sid ~ h~ Ab BY S b bD SUBJECT
- ' A 4 ^8 M'D E g
Checked By Fuel Region Input
- I'd Volume fraction of fuel rods =
, f Node g
(No. of Rods / assembly) x (Area of a rod)
(Area of assembly) 121 (TTRclad )
2
=
^assembly 121 (3.141) (.0 //7ft)
=
0 0.382 0.2286
=
From previous calculation; porosity = 0.28 in fuel region. Thus solid volume fraction in racks = l-0.28 = 0.72. Of this solid volume fraction of 0.72, we know 0.2236 is O
made up of fuel rods. The rest, or (0.72 - 0.2286 = 0.4914), is the solid material (rcck components and non. flow areas) other than fuel rods.
l
- Thus, Volume fraction of unheated =
0.4914 /
)
material in fuel regions O
Number of Rods Per Node Rods per unit pool surface area 121 rods / assembly
=
l 0.582 ft / assembly 2
ds 207.9 j
g
=
2 To get the number of rods in a node r ds (207.9 2 ) gp g g g N
=
rods ft
- O The calculated number of rods per node is displayed below per each value of (I, K).
2 3
4 5
6 7
8 1
.o 7
o.
o.
o.
o.
o.
o.
c.
G G% 654 656 su su sn o*
N WBEft. cf RCCS O
s ens 9;15 ens 632. 632. 682.
o, PER Wots-
'O 9
itu itu ass sa 3%
e%
o, e
h GM IMT B36 to4o tous lou o C.
g 2
ini lHT G35' toyo toyo o<o O.
O,
!I CORPORATION DATE
- q. g,-
CLIENT FILE NO. b N D ~ bA ~ IU BY $ D' M SUBJECT b MW M A'M b Checked By
'O O
Power Factors To make the power distribution both simple and conse vative, uniform axial power distributions were used in all risers.
O To add conservatism, the radial power factor in two nodes (I = 2, K = 2) and (I = 2, K =
- 6) was set to 2.73 which is the maximum local power anywhere in the BRP core. This input results in a total of 1991 fuel rods or approximately 16 fuel assemblies operating at 2.73 times the nominal power level.
Top Surface Heat Transfer O
The heat flow rate out the top surface of the poolin GFLOW is, 9
"sur ^sur (T
~
out top air T
surface temperature of water in pool O
Q*outP-t tal energy fl w rate out of top - equal to pool heat load A
surface area of pool top sw H
user input heat transfer coefficient T[ -
user input air temperature above the pool (width) x (length)=
174 ft A
=
sw O
9out
- 9gen =
(1991x2.73+26503)x73.33 ft. - Ibf.
sec 6
2.34x10 f t. - lbf /
=
sec.
O T.
was selected as 179 F, an arbitary choice. Then the input steady-state value of (r f r input to GFLOW is H*
- As,C.Tro,- L )
i
,O 2.. 59 d IT6 (,"2.\\ 4.- \\1%)
i 1 -\\b4
,e 3 % se+e_qn_sp l
1
!O in the actual GFLOW run H was ramped from 0 to 396. over the first 300 seconds of s
the transient run to avoid Tver cooling of the top surface at early times in the transient.
1 i
!O lQ
O
- HNUS W*A I
!CCRFCAATION DATE R 5 '-
FILE NO. M-Mo BY E
CUENT S
b ' @W bMM6 Checked 8y O
SUBJECT cO Local Loss Coefficients O
Unlike the one-dimensional modeling, GFLOW's three-dimensional modeling accounts for the pressure loss effects of area changes included in GFLOW's input.
Also frictional losses by flow through the bundle and downcomer paths are accounted for by the permeability of the medium. Likewise, the effects of flow direction change are accounted for in GFLOW. However, GFLOW does not account for grid spacers, small flow obstructions and local area changes.
To account for such losses local loss O
coefficients of 2 in each downcomer node, and 11 in each fuel assembly node were arbitrarily selected for flow in the vertical directions. Experience with 1-0 analyses indicates that the results will not be strongly dependent of the values of loss coefficients. In addition, loss coefficients of 9000, were applied for cross flows (X and Z directions) in the racked regions, to account for the vertical flow channels of each riser.
0 7
Results Complete GFLOW input and output listings are given on the computer printouts.
The most important results are summarized in Table 1. Shown as a function of time O
are pool average water temperature and the temperatures of the coolant water in three nodes, (2,2,3), (2, 2, 5) and (2, 8, 5) as a function of time.
Notice that the pool average water temperature reaches 213.5 F at 250 seconds and then remains constant, indicating that energy inflow equals outflow from the pool l
af ter 250 seconds.
lC l
The result of particular interest is the inlet temperature to the risers. Nodes (2,2,3) and (2, 2, 5) are the infer nodes to the two high power regions of the pool. Their I
temperatures are given vs time in the table and never exceed 213 F. Plotted in Figure I is the nodal temperature (2, 2, 5) and the maximum water gemperature for 3 = 2 nodes (elevation below the riser inlet). Neither plot exceeds 213 F.
!O o
l These results indicate that the assumption of 212 F inlet temperature of the bottom l
of the fuel rocks is reasonable. It is noted that the results of this analysis are not intended to be precise indicators of temperature of all locations and times, but rather they are intended to show the nature of the natural circulation flows.
!O llQ l
l i
l l
lC l
l
O I
CORPCRATlCN DME y, 9, g N-O FILE NO. M~W bb BY CLIENT SUBJECT b b'A M M MS Checked By -
M c.
o O
TABLE 1 Results (Temperatures in F, Time in Seconds)
Pool Ave.
S ecific Nodal Temperatures P
Transient Water Temp.
O Time T
(2, 2, 3)
(2, 2, 5)
(2, 8, 5) ave 0
212.0 212 212 212 50 212.4 211 211 212 100 212.8 211 210 215 O
150 213.1 210 210 216 200 213.4 209 206 213 250 213.5 209 208 215 300 213.5 207 207 212 350 213.5 212 208 215 400 213.5 206 205 214 0
450 213.5 209 212 214 500 213.5 211 208 215 550 213.5 208 208 214 600 213.5 204 206 211 650 213.5 209 206 212 700 213.5 208 210 212 O
750 213.5 211 212 214 800 213.5 204 212 217 850 213.5 210 210 213 900 213.5 210 211 213 950 213.5 210 209 214 1000 213.5 209 212 213 O
1050 213.5 208 212 214 f
1100 213.5 210 210 213 l
1150 213.5 207 208 214 l
1200 213.5 209 209 215 gm O
O
O O
O O
O O
O O
O O
O F)6uRG 1 m n blG ll 0 C k VOTNT SQ p / M ity1 u lti J r/ L E T 7 5 M PE'l # WAE
%5 _I.
(
~
vr g
T.TJV1 &
^
i 8
IAMlWM iwdT 7 Eve 6o rmoF, q
gr s=2 No oEs.
E O
(9) 'Isf
/ ec sa z
,gg*p
-=~
-l
~~
L lL'
~
?
it' dj teo N
f 3 ?
[ INA SY TwFE Rkru R 5 l
n To A sssmity
(" " 1, 2, T )
h 10%
=2 o
9*
a 4a a
b d
k o
,sr>
goo zvo toos-12a cC 1'/n1 B Cm)
Page O of
'^4 4
O q_ 2.% g,"
CORPORATION DATE FILE NO. N b"M I'*
BY b -
CLIENT O
SUBJECT W
OODb Checked 8y O
Lgn iwy op C3 ptow gy pq7 gqQ 1500.
O.
50.
.02
- 1. 50-- -
1.
l 1.
-1.
1.
-1.
7.
8.
6.
5.9E 25300.
-- 1. 83 - --. 0854-. 000805 -----
5'.2--
,O l
212.
25300.
.000805
.0166
.0187 1.7 7.53
.01 1921.
1776.-
- 0. 90 8 -- - - - 1.70 -
216.
- 20. 2 - - -
12.7-3 0
1 126 0
2 1
1 3
l 14502.
O.
14502.
400.
14502.
2000. -
179.
212.
O.
.O-390.
300. --
390.
2000.-
O O.
212.
O.
O.
212.
2000.
4.21 4.21 4.21 3.28 3.28 3.28 3.5 1.00 1.5 2.5 3.5 5.345 5.345 5.345 5.345 1.525 1.525 1.30 1.00 0.75
.584 l
.50 1.
.07 g.__
5 5
O 11 5
5 O.
1.
1.
1.
O.
O, O.
O.
- 2. 73- - -
i.
1.
1. -- -
~ -
1.
0.---~---------
l 1.
1.
1.
1.
1.
1.
O.
1.
1.
1.
1.
1.
1.
O.
g, g.;.
- -- --1.
l'.----
- 1.- - - -
-- 1. - --
--0.'----~------
- O 2.73 1.
1.
1.
1.
1.
O.
O.
O.
O.
O.
O.
O.
O.
O.
i
- 1335.-
1335.-
--1335.
-- 1040.- -
1040. --
1040.
O.
1335.
1335.
1335.
1040.
1040.
1040.
O.*
1138.
1138.
1138.
886.
886.
886.
O.
875. -
875. -
375.
-- 682.
68Z --
682.
-O~---------
lO 656.
656.
656.
511.
511.
511.
O.
l 0.
O.
O.
O.
O.
O.
O.
O.
g
. g-7
.5 2.
9000.
.4915 2
5 6
9000.
1~1.
9000. -- ~ 7 4913-
~ - ' -
iO 2
5 5
9000.
11.
9000.
.4915 2
5 4
9000.
11.
9000.
.4915 2
5 3
9000; -- - - --- ~ 1 1 ~. ' - --- 900 0.
.4915 - -
O 2
5 2
9000.
11.
9000.
.4915 i
3
-.g....
7
.5 2.
9000.
.4915 3
5 6
9000. -
- " 11;- - 9000 -
. 4 915---
lO 3
5 5
9000.
11.
9000.
.4915 3
5 --
4---
9000.
11.
9000.
.4915 10 1
i
4 Pagn 1
- of O
i O
N' N RPOREON DATE CLIENT O
FILE NO.b bNO b-BY SUBJECT W
MMM Cheded By O
3 5
3
-- 9000r --- - -- 1 1.
9000. --
.4915 3
5 2
9000.
11.
9000.
.4915 O
4 -
5-7
.5 2.
9000.
.4915 4
5 6
_-- 9ooo;. - -.
1 g,_ _ --- 9 0 0 0.
--. 4915-- - --
4 5
5 9000.
11.
9000.
.4915 0 _ _ 5- - - _ -.. - - -- -- - _
9000.
11, 9000.
.4915 4
5 3
-- 9000.
-- 1 1.
-- 9000.
- 4915--
4 3
2 9000.
11.
9000.
.4915
- O
- s -. _ 7
.5 2.
9000.
.4915 5
5 6
9000.
-- 114 9000.
. 4915-- - --
5 5
5 9000.
11.
9000.
.4915
.O 5
5-
-4 9000.
11.
9000.
.4915 5
5 3
- 9000. - - -
11.
- -- - 9000r - -
. 4915--- *- -
5 5
2 9000.
11.
9000.
.4915 O
6 5
7
.5 2.
9000.
.4915 6
5 6
9000.
11.
9000.
.4915 6
6 5
9000.
11.
9000.
.4915 0
6 5 - -- - -*-
9000.
11.
9000.
.4915 6
5 3
^-- 9000. --
tT. - ~--
900G.
~~. 4915~~ -
6 5
2 9000.
11.
9000.
.4915 0
- y - g.--- g- --..
.5 2.
9000.
.4915 7
5 6
9000; -- -- - - 1 t'.
9000.- ----. 4915 ---
6 7
5 9000.
11.
9000.
.4915 O
7 - - --
9000.
11.
9000.
.4915 7
5 3
9000. -
- 1 1.'
^ - - 9000. - -- - 4915--
O
O CORPORATION DATE N
.p-CLIENT C
FILE NO.
N~N~O bk N-BY b ' b OW kW D Ih SUBJECT Checked By O
7 5
2 9000.
11.
9000.
.4915 8^
5 ~
~
- - ^ - ^
.5 2.
9000.
.5 O
8 5
6
. 5 - -- - - - - - - 2.
9000.
.5-8 5
5
.5 11.
9000.
.5 i
l 8-5 -- - - 4 ~ ^ -- - -
.5 2.
9000.
.5 O
8 5
3
. 5 - -- -
-2.--
- - 9000---
-.5--
8 5
2
.5 2.
9000.
.5 2 - -
7--
.5 2.
9000.
.4915 0
2 4
6 9000r- - - -
11.
9000.--
.4915 -
2 4
5 9000.
11.
9000.
.4915
-- 2 -4 9000.
11.
9000.
.4915 O
2 4
3 9000.-
11.-- - - 9000r -
. 4915-- -
l 2
4 2
9000.
11.
9000.
.4915
. 4-7 - -- --
.5 2.
9000.
.4915 O
3 4
6 9ooo,___... _
g1.._
_._ 900o.,_
-_,4915 --
3 4
5 9000.
11.
9000.
.4915 l
3 -
4 4----
9000.
11.
9000.
.4915 g
3 4
3 9000.-- --
11.
-9000.- -
.4915 3
4 2
9000.
11.
9000.
.4915 4
4-.
7
.5 2.
9000.
.4915 4
4 6
O 9000.
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