ML20153G346
| ML20153G346 | |
| Person / Time | |
|---|---|
| Site: | 05200003 |
| Issue date: | 09/22/1998 |
| From: | WESTINGHOUSE ELECTRIC COMPANY, DIV OF CBS CORP. |
| To: | |
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| ML20153G343 | List: |
| References | |
| NUDOCS 9809300043 | |
| Download: ML20153G346 (71) | |
Text
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5 3.2 The Eckert and Diaguila Mixed Convection Heat Transfer Tests
- N po assare. a cockad ve\oN)
Eckert and Diaguila* conducted heat transfer tests on a vertical tube that was 13.5-feet high with a 23.25-inch inside diameter. Inlet and outlet air pipes and dense screens were located at each end. A 10-foot steam jacket supplied steam slightly superheated as the heat source. Sixteen condensation chambers collected and piped condensate to a station where the flow rate was measured and the local heat flux was determined. An air flow at approximately 80*F, at pressures from 1 atmosphere to 99 psia, was forced through the test section. Tests were conducted with forced flow in both the opward (assisting mixed convection) and downward (opposed mixed convection) direction.
Thermocouples at the tube center and in the tube wall provided a temperature difference from which the local heat transfer coefficient could be determined. The test data were used to validate the mixed convection heat transfer correlation at prototypic Reynolds and Grashof numbers. i l
The Nusselt number, Nu, is defined as Nu = hdA, whereh d is the hydr"& 6 aeter. Entrance-effect multipliers were calculated as described in Secdon 2.2 and are prev.ma tn Table 3.2-1. The mixed convection Nusselt numbers were calculated as described in Section 2.1. The calculated Nusselt l number for each of the ten assisting convection tests are compared with the measured data, and are shown as a function of the dimensionless height in Figures 3.2-1 through 3.2-10. The relevant test parametcrs are preanted in Table 3.2 2.
l TABLE 3.2-1
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ENTRANCE-EFFECT MULTIPLIERS FOR THE ECKERT AND DIAGUILA HEAT TRANSFER TESTS Distance from bottom, ft 0.63 1.25 1.88 2.50 3.13 3.75 4.38 5.00 5.63 6.25 6.88 7.50 8.13 8.75 9.38 10.0 Muloplier 2.89 1.44 1.30 1.24 1.20 1.17 1.15 1.14 1.13 1.12 1.11 1.10 1.10 1.09 1.09 1.08 for d3 =
1.94 ft.
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As discussed in the reference report, heat flux to the plate was determined experimentally using heat flux ineters and by performing coolant energy balances, resulting in an uncertainty within m 3 percent associated with the reported heat flux measurements.
Chromel constantan (Type E) thermocouples were used for all test temperature measurements.
Assuming a typical Type E thermocouple accuracy of 2 0.5'C and an instrumentation error of 2 0.02*C results in a total uncertainty of 2 0.5'C or z 0.9'F.
Duct air velocity measurements in the Wisconsin Condensation Tests" were obtained using a pitot tube and pressure transducer as in the Westinghouse Flat Plate Tests" Assuming instrumentation similar to that considered in Subsection 4.5.1 was used in the Wisconsin Condensation Tests and that the resulting air velocity measurement uncertainty of 0.32 ft/sec is typical for the range of recorded test velocities results in an air velocity measurement uncertamty of 0.32 ft/see or 0.098 m/sec.
These test measurement uncertainties result in measured Sherwood number uncertainty within z 12 percent for the reported University of Wisconsin condensation tests".
4.4.4 Open Literature Tests 7.AfofNk.On on A Afncertainties in the Hugot"", Eckert and Diaguila"', Siegel and Norris"", Gilliland and Sherwood*,
- and Chun and Sebanm tests as*4seussed-4ade open literature references.
A IS livm M h v4 O M prov'sded in O CSC.
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Re AP600 riser channel differs from the test geometries due to the 6-foot well, or turning region at the bottom of the baffle. For modeling simplicity it is desirable to use a fully-developed heat transfer coefficient over the full channel height. The following subsections show the use of a fully-developed heat transfer coefficient over the full riser height is conservative. The calculations show the heat transfer decrease (relative to fully-developed heat transfer) is more than offset by the heat transfer increase due to neglecting the entrance effect in the channel above the well. The geometric features of the well region and riser channel are shown in Figure 2.1-4. l l
l l
2.2.1 Heat Transfer in the Well Region Below the Baffle l
The annular duct created by the baffle for the AP600 starts 6 feet above the bottom of an annular p "well." his well is[ feet wide and is heated on the inside surface. In the AP600 evaluation mode is assumed, for simplicity, that the forced convection heat transfer correlations used in the annular region can be applied within this region as well. It is more realistic to assume a free convection heat transfer relationship on the heated containment shell side of the well.
Although the upper half of the 6-foot height may undergo transition to turbulent free convection, the l
laminar free convection correlation predicts lower heat transfer coefficients and is used. De effect of using forced convection in the 6 foot well is evaluated by comparing the total heat transfer calculated with laminar free convection in the well to the total heat transfer calculated with forced convection everywhere.
De empirical formula of McAdams W was chosen for the laminar free convection mean Nusselt number Nu = 0.555(Ra,)!'d (8) ne Nusselt number for forced flow convection is O m by the Colburn W relationship:
Nu = 0.023Re % l'3 (9)
Assuming the active length of the annulus above the baffle is 90 feet, then the active heat transfer length is % feet. De fractional decrease in total heat transfer over the 96-foot height due to free convection in the 6-foot well region is equal to the factor $ detertnmed by length weighting.
Equations (8) and (9):
Ra x l 'd 6
1 2(.555) (10)
& = 96 6(.023) Re'O Pr 1/12 ,
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l N Chimney L
Weir # I I
( HContainment Riser -
-G i Shell Downcoraer - -g l
jl Baffle 96*
il Shield Building l
Annular Channel Entrance 3 l 't Well Region 6' ,,
I h
/
e Figure 2.14 PCS Air Flow Path Features aw2. wpr;it>ag97 R
,9 Qs Q
_ _ _ __ _ . - ._ . _ _ _ _ _ _ _ _ . . . . _ _ . . _ . _ . .-m _ . _ _ . _ _ . _ _ _ . _ . . . _ . _ . . . . _ . _ _ _ . . . _ . . _ . _ _
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O 5000 10000 1$000 20000 25000 m
. Test Cass -Mean(0.sas)
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p ae Figure 3.6 2 Comparison of Predicted.to Measured Evaporadon Rates for the GilHInnd and Sherwood Evaporation Tests o \3542w4wp(:11450597 Revuaan 1 3-47 . _ _ _
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- 14. Eckert, E. R. G., Drake Jr., R. R., Analysis of Heat and Mass Transfer.1972, McGraw-Hill.
4
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- 15. Kestin, J., et al.,1. Phys. Chem. Ref Data, 13, 229, 1984.
- 16. Rohsenow, W. M., Hannett, J. P., Handbook of Heat Transfer,1973. McGraw-Hill.
- 17. Bird R. B., Stewan, W. E., Lightfoot, E. N., Transpon Phenomena,1960, John Wiley & Sons.
- 18. "WGOTHIC Application to AP600," WCAP 14407, Section 3, September 1996, Westinghouse Electric Corporation.
- 19. Siegel, R . Norris, R. H., " Test of Free Convection in a Penially Enclosed Space Between Two Heated Vertical Plates," Journal of Heat Transfer, April 1957.
- 20. Stewater, W. A., Pieczynski' A. T., Conway, L. E., " Tests of Heat Transfer and Water Film Evaporation on a Heated Plate Simulating Cooling of the AP600 Reactor Containment,"
WCAP-12665, April 1992, Westinghouse Electric Corporation.
- 21. " Heavy Water Reactor Facility (HWRF) Large-Scale Passive Containment Cooling System Confinnatory Test Data Report," HWRF-RPT 93-001, July 1993.
- 22. Gilliland, E. R., Sherwood, T. K., " Diffusion of Vapors into Air Streams," Industrial and Engineering Chemistry, Vol. 26, No. 5, pp. 516-523.
- 23. Huhtiniemi. I., Pernsteiner, A., Corradmi, M. L., (University of Wisconsin), " Condensation in the Presence of a Noncondensable Gas: Experimental Investigation," WCAP-13307, April 1991, Westinghouse Electric Corporation.
h 24. Peters, F. E., " Final Data Repon for PCS Large-Scale Tests, Phase 2 and Phase 3,"
WCAP-14135, 22,1^^t, Westinghouse Electric Corporation.
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i Revwee 1 eM542=.5 wpf Ib 050597 May 1997 7-2
4.5 Mass Transfer Correlation Biases s
Re~ mass transfer correlations selected for use on AP600 were compared to data from both SETS and integral effects tests (IETs). The data comparisons were presented in the form of predicted-to-l measured Sherwood numbers. The comparisons show the correlations underpredict the data with mean predicted-to-measured values of 0.936 for evaporation and 0.988 for condensation. Thus, the selected correlations exhibit an underprediction of the mean data.
As a conservative approach the correlations can be biased, =512: .h 2- - p; int in: --- mee e crpxf r u uA'5 $; .:.. ...: x=!d= - - t=rds H i; . ... r.dcr of 1,. . !--- ;;; i;-
" ~' - p t f : -> '"ta; .;, i: 5 ; J euc; "! x b,~ c.de .:: i ; ' - This can be expressed as: -g CP s1 (21)
M where:
I
- C is the bias factor P is the predicted mass trsnsfer coefficient value M is the measured mass transfer value Rus, the value for C can be determined from the most overpredicted data point as: l l
C5EP (22) i l
l De evaporation test data are plotted in Figure 4.2-3 and have a peak value of P/M = 1.191. Thus, the value of the bias factor for the evaporating data is C = 0.840. By _'id;!% ; i: n ,~.i- --~ Y
_,g,,, c;.7!9 hy ,hi, m.~ k. mm w e :: .x .;.ic;;y 9: 2; .;; - -'"ca p7d:M.
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. c; ~.J Shen,~d c. r.ir _'~i: d di i i:x'.in; x=, !dx .. ,;m... ... P.; a 4.2 . - $
. ,~ .. ~ .c g .--_
ne condensation test data are ploued in Figure 4.3-3 and have a peak value of P/M = 1.541. His particular value lies somewhat above the bulk of the data and wi wds to a single elevation on the LST, while five other simultaneous measurements at different elevations in the same test produced lower P/M values, nis peak value is considered a local anomaly that does not represent integral condensation rates.
Consequently, the next highest value, P/M = 1.369 was selected for evaluatmg the bias factor. Rus, the value of the bias factor for the' data is C = 0.730. By rfphi; t: xd-~-t. c..;; - $-
^ rjar - -bh by 12^ fr~. i G . _'i ; . x ;__."/ .ic;'y P' '- i; ;;;" '^" N =-f_
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ATTACHMENT 2
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d Markups to WCAP 14845 Hov 2, " Scaling Analysis for AP600 Containment Pressure During Design Basis Accidents" (Page E-5): The data table, which supports statement on validation of equation, is no longer part of the report. Was Table 10-8, Section 10.2.1.1.
RESPONSE
The second bullet on pg. E 5 refers to the mean devhtion of less than 0.01 and the j standard deviation of 0.13 which were provided in Table 10-8 of WCAP 14845, Rev. O.
This table was deleted from the revised scaling report because the information in the I table was not needed to support the results of the top-down system level scaling described in Part lli of the revised report. The second bullet on page E 5 is an accurate i statement that is supported by a Westinghouse calculation note. Descriptive text and the l l
information from Table 10-8 (from WCAP-14845, Rev. 0) will be added as a new appendix. Reference to this new appendix will be added to the second bullet on page E-5.
(Page E-8): The is no Fqure 11 1. Is it 10 5?
RESPONSE; l Figure 11 1 should be Figure 10-5. The Scaling Analysis document will be revised to l -
change the references to Figure 11 1 on pages E-8 and 12-3 to Figure 10-5.
i s l (Page E 8): Last paragraph. Where and what is the support, code version (1.x,4.x), models (LP,DP, errors), etc.? In wha section (sections) can this material be found?
RESPONSE
t i WCAP 14845 will be revised to define the Evaluation Model by reference to WCAP-
'4407. Rev 1, Section 4.
i 1
(Page P 2): Thought GOTHIC was selected but needed additional model for the clime.
WGOTHIC was result of effort.
l
RESPONSE
The sentence in question will be revised to state that GOTHIC was selected as the best l
available tool. The third paragraph under " Element 1" will also be revised.
1 (Page P-4): LST ref, is old June 1994 report. April 1997 revisions indicates potential for bad i analyses if based on original.
l RESPONSE-1 i
The test data used in the Scaling Analysis are all consistent with the April 1997 issue of WCAP 14135, Rev.1. Reference 10 on page 141 will be corrected.
WCAP.14645. Rev. 2 Markups I
(Page P-6): Distributed parameter model? Role and status. Is there a summary or which sections describe use of this model?
RESPONSE
The reference to the distributed parameter model will be removed from WCAP-14845, page P-6.
(Page 1-5): Ref. to Ref. 47 Should be Ref. 5. Section 9 of 4 is not to be reviewed.
RESPONSE
Yes, Reference 4 should be Reference 5. WCAP 14845 will be revised to refer to Reference 5.
(Page 21): What is the mixing and stratification report? Section 9 of WCAP-144077
RESPONSE
Yes. WCAP-14845 will be revised to change " mixing and stratification report" to Reference 5. Section 9.
(Page 8 3): There is no shading visible on Table 8-3, or any other table (8-4 and 8-5), to indicate > 10%.
RESPONSE
WCAP 14845 will be revised to correct the discrepancy. The shading will be added to the tables.
(Page 10-5): 2%, is it non-conservative?
RESPONSE
WCAP 14845 will be revised to note that the Colbum correlation used for AP600 predicts 2% higher heat transfer coefficients than does Dittus-Boettar, or Seider-Tate. The Colbum correlation differs little, but is 2% less conservative than the attematives.
(Page 11-6): There is no Table 1010. Table 10-37
RESPONSE
Yes, WCAP 14845 will be revised to change Table 10-10 (2 places) to Table 10 3.
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I WCAP 1484s, Rev. 2 Markups i, 2 i
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Westinghouse has prepared AP600 Response to Requests for Additional Information as an ;
enclosure to letter NSD-NRC-97-5216 of June 27,1997. The majority of the responses appear to l s be acceptable. However, comments and clanfications apply to the following RAls:
(1.) (RAI 480.975) Pi-groups pip ,g,j and pie ,f,jf have not been replaced in Table 21 as stated in the response. Please clanfy where numerical values for these pi-groups can be found.
RESPONSE
The subscript "p,g,j" should be p,q,j, which indicates a pressure pi group, p, for sensible (radiation plus convection) heat transfer, q, from heat sink j. j is an index that represents the heat sinks listed in Table 7-1. Values of p p,q,j are presented for each time phase in Table 8 5. WCAP 14845 will be revised to correct this subsenpt error in Table 2-1.
WCAP-14845 will be revised to replace the group pe,f,ifby pe,f,j and pe,q,ssx to be ;
consistent with Note 1 to Table 2-1.
i (2.) (RAI 480.995) In the previous revision of the scaling report, the Biot number had been calculated to be 0.08. Now it has been recalculated as 0.13. According to Kreith, Principles of Heat Transfer",3rd ed., p.140, a criterion for treating a heat structure as a lumped mass is that the Biot number be less than 0.1. Since Kreith's criteria is no longer satisfied, what is the justification for lumping the steel? What is the estimated magnitude of the error introduced by this approximation?
RESPONSE
Kreith's Biot criteria Bi < 0.1, is based on a temperature error of less than 5% It is estimated that Bi < 0.13 would give a temperature error of less than 10%. Such an error is considered acceptable for a scaling analysis in view of the simplicity of the lumped parameter assumption. l Westinghouse will review the use of Biot number and the discussion provided in the Heat
& Mass Trarsfer Report, the PIRT, and the Application Report. Text will be updated as needed for consistency and clarification.
(3.) (RAI 480.1002) There still appears to be a problem with the nomenclature in equation 135 and in the equation on the second line of page 7-30. Why is it necessary to change the temperature subscripts in going between these two equations? Also, the subscript " sex" (not in the nomenclature section or in Figure 7-3) is not defined.
RESPONSE
WCAP 14845 will be revised to replace the undefined subscripts sc and scx with the defined subscripts ss and ssx. That will correct the inconsistency in Equation 135 and the equation on the second line.
1 (4.) (RAI 480.1011) The stated revision to the text does not appear to have been made.
RESPONSE
WCAP-14845 will be revised to state that the nser and downcomer both operate in forced convection, consistent with Figure 41.
i l WCAP 14845. Rev. 2 Markups
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. -- _- - ~ . . - - . - - - . . . . - - - . . . - - - . _ . . . - . - . - . . - - - . .
R.
(5.) (RAf 480.1017) The RAI was directed toward determining whether any of the remaining
_ , . pi-group values contained an anomaly similar to that for pic ,bf. The NRC review did not check the value of every pi-group. Please provide an evaluation of the anomaly effect for piic,dsx and pic,esx-
RESPONSE
Although the pi value may appear anomalous, the temperature and heat transfer rate calculations are correct. The individual heat transfer coefficients and the corresponding temperature differences for the baffle inside, the dry shell outside, and the evaporating shell outside are presented in Table 1. The values show the convection and radiation heat transfer coefficients range from 1.5 to 2.7, a reasonable range. When multiplied by the corresponding DT the heat transfer rate is also reasonable. However, when the small negative riser to-baffle temperature difference is used to normalize the baffle heat transfer rate the anomaly appears. The anomaly only appears in the baffle equation since the evaporating and dry shell DT's are all relatively large values.
The selection of a different normalizing temperature difference would change the apparent anomaly for the baffle, but would not change the resulting temperatures and heat fluxes. Or, as stated in RAI 480.1017, expressing the energy equation in terms of 1
the riser baffle and shell baffle temperature differences instead of only the riser-baffle temperature difference would also e!iminate the anomaly.
3
- Table 1 -Temperature Differences and Heat Transfer Coefficients for the Shell and j Baffle Evaporating Shell Dry Shell Baffle Evaporation Energy hm,esx = 126.6 hm,ri-bf =0 4
Transfer DTxf-ri = 41.62 DT r;-bf =-0.04 Convectico Heat he,esx = 2.73 he,dsx = 2.67 hc,ri-bf =2.47 Transfer DTxf-ri = 41.62 DTdsx ri = 113.21 DTri-bf =-0.04 Padiation Heat br,esx= 1.50 hr,dsx = 1.78 hr,shx-bf = 1.60 Transfer DTxf bf= 41.58 DTxt.bf = 113.17 DTshx-bf = 41.59 Liquid Film Heat hxt= 840 Transfer DTxf-bf= 6.49 4
J i
1 4
WCAP.14845. Rev. 2 Ma*ups 4
- 6. (RAI 480.1026) Why does increasing heat transfer coefficient with increasing Reynolds
- Number imply that there is no concern?
RESPONSE
Our understanding of the concerns expressed in the RAI are that the test data range does not cover the AP600 range, and that the heat transfer coefficient may misbehave at higher Reynolds numbers. The Chun and Seban data cover Reynolds numbers up to 20,000, or approximately 5 times higher than the highest AP600 Reynoids number, so it is clear the data cover the AP600 range. The test data sow the Nusselt number and heat transfer coefficient continue to increase uniformly as the Reynolds number increases, and that the correlation models the data. Consequently it is highly unlikely that the minimum heat transfer coefficient value has been missed. ,
1 (7.) (RAI 480.1027) In addition to the information in the RAI, the following is needed to complete the review. Please compare the physical film thickness (as predicted by the Nusse!t equation) to the Chun and Seban effective film thickness over the range of l
Reynolds Numbers expected for AP600 (both inside and outside the PCS, above and '
below the second weir). For each Reynolds number, compare the heat transfer coefficient for the water film using the Nusselt model to the Chun and Seban model. I 1
The wording in the first paragraph of Section 7.4 has been improved to distinguish the )
effective film thickness from the physical film thickness. Unfortunately, in the second l paragraph, the effective film thickness is used to get the heat capacity of the film, I whereas the physical thickness should be used. The difference in the ratio calculated is I not significant, but it confuses the issue, in the sense that it encourages the reader to thing of the effective thickness as a physical distance.
RESPONSE: l 1
The Nusselt equation models the smooth laminar film flow that exists for film Reynolds !
numbers less than 30. Consequently it is not appropriate to apply the Nusselt correlation to wavy laminar and turbulent film flows. The result of misapplying the Nusselt smooth laminar film correlation to higher Reynolds numbers is to predict a thicker film with lower heat transfer coefficient than given by the Chun and Seban correlation.
S"ce the heat capacity of the liquid film depends on the mass of liquid, a measure of the l average film thickness is needed to estimate the volume and resulting mass. The l effective thickness, determined from the film heat transfer coefficient correlation, is a reasonable measure of the average thickness. In light of the small value of the estimated heat capacity, and the transient energy storage, a me,e rigorous measure of the average film thickness is not required.
Westinghouse will add Kutataladze cata to Figure 10-3 of the Scaling Report to provide further basis for the nominal Chun and Seban correlation. In addition, further justification in the text will be provided. This willinclude a discussion of the distinction between physical and effective film thickness. Westinghouse will also perform a sensitivity calculation varying film thickness to confirm the Low ranking of this phenomenon.
WCAP 14845. Rev. 2 Matups 5
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- (8.) (RAI 480.1031) in Table 10-3 the new footnote reveals that for LST, measured air / steam a concentrations were used since LST is not homogeneous. How were air steam concentrations for AP-600 determined for use in calculating the pi-group values? i l
RESPONSE
1 1
The AP600 air / steam concentrations were determined from the Scaling Model, that ;
assumes the total mass of gas is well mixed. Westinghouse will add a reference to I Appendix 9.C of the WGOTHIC Application Report and also include a summary of the hand calculation results related to stratification gradient.
i 1
- 9. (RAI 480.1032) The definition of distortion provided appears to be appropriate for phenomena which are quantified by pi-groups. However, some phenomena. such as mixing and stratification are not represented by pi-groups. A broader definition of .
distortion appears to be needed to cover phenomenon not quantified by pi-groups. l l
RESPONSE: l Westinghouse has used conventions and definitions from the literature as guidance for the containment pressure scaling analysis. The literature typically defines distortion in terms of pi groups, so there is no known convention for defining distortion for groups that appear as parameters in pi groups, rather than as pi groups.
(10.) (RAI 480.1035) Reference to the WGOTHIC Application Report, Appendix 7.A, which you l state was added could not be found. The reference citation should appear in the section titled 'Extemal Water Flow Time Variations' on page 117.
RESPONSE
WCAP 14845 will be revised to include a reference to WCAP 14407, Rev.1, Section l 7.6.3, that includes the maximum and minimum film flow rate values, and the uses for the values. (Since RAI 480.1035 was written, WCAP-14407 was revised.) l
- 11. (RAI 480.1036) The conclusions still appear to be somewhat disjoint from the main body of the report. For example, the discussion in item 1 would seem to be supported more by the Applications Report than this Scaling Report.
RESPONSE
The discussion in Conclusion item 1 identifies the high and medium ranked phenomena that were confirmed by the scaling analysis. The conclusions also provide information from WCAP 14326 and WCAP-14407 that tells how the phenomena are conseaatively modeled. Westinghouse will add summary statements for each of the referenced sections.
WCAP 14845. Rev. 2 Markups 6
l l E-5 l
l Top-Down System-Level Scaling l l
l The comparison shows the scaled LST captures the high ranked phenomena associated l with the AP600 containment pressurization during blowdown. However, internal field characteristics during and after blowdown cannot be predicted with the lumped parameter evaluation model.
Nominal predictions of the steady-state scaling equations using free convection heat and mass transfer inside containment and measured air / steam concentrations for 21 steady-state LST cases show the average steady-state mass and energy transfer rates are i predicted with a mean deviation of less than 0.01 and a standard deviation ofP0.13. (A PEA A Such agreement is considered to verify that the mass and energy equations accurately ,
g predict the transfer rates, thereby validating the mass and energy scaling equations.
The transient RPC equation is the result of combining the mass and energy rate equations with the equation of state. At steady-state conditions, the terms on the right-hand side of the RPC equation represent the equivalent mass and energy rate terms.
Therefore, validation of the steady-state scaling equations implicitly validates the RPC equation.
The detailed breakdown of individual pi groups shows that during all the phases of a i DECLG LOCA, phenomena associated with the drops, pools, clumney, and baffle are not important and can therefore be neglected since the pi group numerical values are of
. order less than 0.1. The only pi groups of any significance are those associated with the solid internal heat sinks and the shell. These internal heat sinks become saturated prior l to the time when quasi-steady operation occurs. Therefore, only the pi groups l identified as containment or shell are calculated for the AP600 plant and LST at steady-state. The LST was scaled to AP600 at a steady-state corresponding to conditions in AP600 expected at 4000 to 5000 seconds into the transient. The scaling comparison shows the dominant terms are the source, condensation, and evaporation, all of which scale to within 8 percent.
Differences and Distortions between the LST and AP600 The LST heat sink area / volume ratios and flow history do not scale to AP600 and thus prevent the use of the LST as a transient IET representation of AP600. However, those distortions do not prevent the use of the LST results to validate the high-ranked, separate effects phenomena of condensation mass transfer and liquid film stability and l coverage. The temperature and concentration measurements from the LST provide some of the data needed to understand and bound stratification in the AP600 evaluation model. Heat transfer measurements from tests with no external water provided data to validate dry heat transfer to the riser. In addition, the steady-state LST results are used to validate separate effects aspects of the evaluation model.
l Execuuve Summary Revtston 2 o43703w.a wpt ItH)62497 June 1997
APPENDlX A Validation of Steady-State Mass and Energy TriWfer Equations
~
The constitutive equations for steady-state heat and mass transfer inside and outside the LST were coupled and solved using properties measured on the LST as boundary conditions. The containment total pressure, steam pressure, and bulk temperature defined the state inside the LST. The riser gas velocity, bulk riser gas temperature, wetted fraction, and the external water flow rate and temperature define the state outside the vessel. The heat and mass transfer rates inside and outside were calculated for the subcooled, evaporating and dry regions.
The measured values for th,,,,, and rh,gh,.a. were used to normalize the predicted values, respectively, for mass and for energy that define the pi values in Equations (199)..
The results are summarized in Table A-1 for 21 LST cases. All tests are included that had measured steam concentrations and the steam source located under the steam generator model. The results show the average quasi steady state mass and energy transfer rates are very close to zero, with a standard deviation of 0.13. Such agreement is considered good for such a simple model. These results verify that the mass and energy equations used in the scaling analysis accurately predict the transfer rates, thereby validating the equations.
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Table A-1 Energy Rate of Change Equation Comparison to Steady State LST w/
Large-Scale Pressure ri1 ih,,, 1 I(n,y+x,y Test pela Temperature 'F STU/sec + x..J 1 I x.a 212.1 A 23.77 334.3 427.2 -0.167 -0.197 212.18 29.36 317.8 667.8 0.058 0.076 l 212.1C 36.93 317.7 963.4 -0.030 -0.948 1
213.1 A 23.5 334 3 398.2 -0.185 0.213 1 213.18 28.83 327.0 642.1 0.039 0.022 213.1C 40.29 319.6 980.6 0.324 0.321 216.1 A 32.44 326.5 706.7 -0.173 0.206 216.1B 50.18 329.1 711.7 0.092 0.068 l 217.1 A 42.37 314.9 1320.7 0.142 0.141 2171B 50.86 319.7 1303.9 0.116 0.115 218.1 A 42.44 314.0 1329.4 0.051 0.047 i
218.18 50.05 317.6 1250 3 -0.001 -0.001 219.1 A 34 97 343.0 145.9 0.082 0.088 219.18 41.89 343.8 148.1 0.086 0.102 219.1C 23.24 340.2 143.8 0.001 0.016 221.1 A 19.36 339.6 185.7 0.117 -0.132 221.18 26.02 333.2 189.5 0.089 0.000 221.1C 63.36 336.7 186.0 0.098 0.106 222.1 99 66 331.1 719.1 0.158 -0.167 224.1 45.51 298.9 309.5 -0.118 0.064 224 2 55.54 310 4 712.2 0.106 0.087 Average = -0.00001 0.004 Standard Deviation 0.128 0.133
M .
The scaling analysis shows the three primary drivers, or dominant system level phenomena, for the pressure transient are the break source, the gas volume, and the l
heat sink surface area dependent condensation rate. The scaling analysis shows the system response is well scaled (properly weights dimensionless groups for these three h dommant phenomena as shown in Figure Midr small values of dimensionless time j and for longer values of dimensionless time, and shows a distortion for intermediate times. The magnitude of the distortion in the mid-range is too large to claim the LST l pressure transient directly scales to AP600 in this range. However, the distortion is small enough that the IST data can be used to examine known lumped parameter modeling biases in the bounding evaluation model.
Furthermore, testing the evaluation model against a range of LST cases, with step changes in boundary conditions (source flow rate, external fan, external water on or off) I is expected to cover the range of system level dimensionless groups for AP600 operation through the refill and peak pressure time phases between the blowdown and quasi-steady long term operation. This coverage is expected because the boundary condition variations result in a range of relative values of condensation rate and steam pressure.
h Asa, dea : MCercue8 5, 6ech 9 The lumped parameter Evaluation Model concentration fields due to its simplified [does not resolve inte momentum model and large lumped volumes.
Comparisons between early versions of the evaluation model and the system level LST
~
response showed that pressure was reasonably well predicted, with a modest l
conservative margin. Examination of internal processes clearly identified the existence of competing internal effects in which the excessive velocities predicted by the lumped parameter model overpredicted the velocity component of mass transfer, while )
overuuxmg underpredicted the steam concentration component of mass transfer.
Consequently, it is required to address competing effects in AP600 predictions. The effect of overpredicted velocities was easily resolved by using only free convection for internal heat and mass transfer, thereby elimmating velocity from the condensation correlation. The ovenruxmg issue was resolved by careft"v evamuung and biasing the effects of circulation and stratification in the evaluation moc n 'iscussed in Reference 5, Section 9.
Executive Summary a:\3ha.wpub.062397 Revision 2 June 1997
12-3 l
The scaling analysis shows the three primary drivers, or dominant system level l phenomena, for the pressure transient are the break source, the gas volume, and the l
~
heat sink surface area dependent condensation rate. The scaling analysis shows the system response is well scaled (properly weigh dommant phenomena as shown tar in small Figure IM)gimensionless groups for values of dimensionless time and for longer values of dimensionless time, and shows a distortion for intermediate times. The magnitude of the distortion in the mid-range is too large to claim the I.ST l pressure transient directly scales to AP600 in this range. However, the distortion is small enough that the LST data can be used to examme known lumped parameter I modeling biases in the bounding evaluation model.
Furthermore, testing the evaluation model against a range of LST cases, with step changes in boundary conditions (source flow rate, extemal fan, external water on or off) is expected to cover the range of system level dimensionless groups for AP600 operation through the refill and peak pressure time phases between the blowdown and quasi-steady long term operation. This coverage is expected because the boundary condition variations result in a range of relative values of condensation rate and steam pressure. 1 The lumped parameter Evaluation Model does not resolve internal velocity and concentration fields due to its simplified momentum model and large lumped volumes.
Comparisons between early versions of the evaluation model and the system level LST response showed that pressure was reasonably well predicted, with a modest conservative margin. Examination of internal processes clearly identified the existence of competing internal effects in which ths excessive velocities predicted by the lumped I parameter model overpredicted the velocity component of mass transfer, while overmixing underpredic+ed '.ne steam concentration component of mass transfer.
Consequently, it is required to address competing effects in AP600 predictions. The effect of overpredicted velocities was easily resolved by using only free convection for internal heat and mass transfer, thereby elimmating velocity from the condensation correlation. The overrruxmg issue was resolved by carefully examuung and biasing the effects of circulation and stratification in the evaluation model as discussed in Reference 5, Section 9.
l l
Conclusions Revision 2 o:\3703w.d wphlb-062397 June 1997
Review by representatives of industry, academia, and regulatory agencies were incorporated into the process. The end result is documentation that describes the PCS DBA evaluation l
l
' ~ model and its bases in an auditable, traceable manner. Following is a brief description of the four major process elements.
Element 1 Determine AP600 PCS Modelling Requirements l The PCS DBA methodology development process began with a review of the AP600 design l and DBA scenarios and an identification of phenomena important for AP600 contamment pressurization. This review identified several separate effects tests (SETS) to investigate specific phenomena such as the liquid flow over the outside of the containment shell, and l
condensation and evaporation mass transfer. In addition, integral effects to:,ts (IETs) at two different scales were also identified to examine the integrated heat and mass transfer behavior of the PCS. The need for such tests was recognized and testing was initiated in the late 1980's. Table P-1 was used to identify the containment phenomena unique to AP600 and l
the tests required to validate models of those phenomena. From this review, the l 4 *?=Sgh GOTHIC G2COE"Cy computer code was selected as the best available tool to evaluate contamment pressure.
A phenomena identification and rankmg table (PIRT) is developed to identify the key thermal-hydraulic phenomena which govern the transients of interest. To allc,e definition of the relevant phenomena, plant design parameters and design basis scenarios are first defined.
The PIRT (Reference 3) then ranks phenomena according to their relative importance to the particular transient phase of interest. The PIRT process included input and review by representatives of industry, academia, cross-functional Westinghouse technical reviews, and regulatory authorities. The bases for high, medium, and low rankmgs are documented in Reference 3 which also documents evaluation model requirements and approaches to address and bound important phenomena. A key result of the PIRT is that the dommant phenomenon for transferring energy from the containment is mass transfer - condensation on the inside and evaporation on the outside. Phenomena ranked high or medium during any accident phase are investigated, and methods to bound uncertainties are developed (see Element 3 below). Phenomena with a low rankmg do not significantiy influence the contamment pressure response; thus, models that capture the gross behavior are sufficient, and where justifiable, a low ranked phenomenon may be neglected entirely. Section 2 summarizes the PIRT high and medium ranked phenomena and the approach that is used to address each.
r As A <ce, M WehgWe.- Go-ML.-
g (Ncicermc. core. m c,eaa,,
The THTC computer code was =b=d, upgraded, =d h to allow explicit modeling of many of the phenomena identified in the initial review. As the scaling analysis and testing programs progressed, code upgrades to better model experimental results were
{ completed according to guidelines consistent with life-cycle management identified in Preface Revision 2 oa3703w-b.wpeit>462397 June 1997
14-1 l l
14 REFERENCES l
, 1. NSD-NYC-97-4968, AP600 Passive Containment Cooling System Design Basis Analysis Reports ' .nuary 31,1997.
- 2. "AP600 Standard Safety Analysis Report," June 26,1992, Westinghouse Electric l Corporation.
- 3. M. J. Loftus, D. R. Spencer, J. Woodcock, " Accident Specification and Phenomena Evaluation for AP600 Passive Containment Cooling System," WCAP-14812, Rev.1, June 1997, Westinghouse Electric Corporation.
- 4. D. L. Paulsen, et al., "WGOTHIC Code Description and Validation," WCAP-14382, l
May 1995, Westinghouse Electric Corporation. '
$ 5. D. L N '--- ? d, "WGOTHIC Application to AP600," WCAP-14407, Rev 1,
% 1997, Westinghouse Electric Corporation.
July
- 6. NTD-NRC-95-4563, " GOTHIC Version 4.0 Documentation," September 21,1995, Westinghouse Electric Corporation.
i
- 7. NTD-NRC-95-4577, " Updated GOTHIC Documentation," October 12,1995, Westinghouse Electric Corporation.
l
- 8. NTD-NRC-95-4595, "AP600 WGOTHIC Comparison to GOTHIC," November 13,1995, i Westinghouse Electric Corporation.
l 1
- 9. R. P. Ofstun, " Experimental Basis for the AP600 Contamment Vessel Heat and Mass Transfer Correlations," WCAP-14326, Rev.1, May,1997, Westinghouse Electric Corporation. I g 10. F. E. Peters, " Final Data Report for PCS Large-Scale Tests, Phase 2 and Phase 3,"
WCAP-14135 *.~'4, Westinghouse Electric Corporation.
3 ; !, l IW.i.3 Aged % l
- 11. NUREG/CR-5809 EGG-2659, "An Integrated Structure and Scaling Methodology for Severe Accident Technical Issue Resolution," INEL, EG&G Idaho, Inc.
- 12. W. Wulff, " Scaling of Thermohydraulic Systems," BNL-62325, May 1995, Brookhaven National Laboratory.
l References Revtsion 2 o:\3703w-d wptit>.062497 June 1997
P-6 Gilliland and Sherwood evaporation tests. These tests, as described in Reference 9, provided additional data to validate models for convective heat and mass transfer in AP600.
.pr b l Code capabilities have been examined using be lumped parameter and dbdLRd p'r xk.: formulation /. The PCS test data and other data from the literature were used to provide input to code validation (Reference 4). The lumped parameter codes oversimplify the flow field by assummg a homogeneous mixture exists within each node. Since lumped parameter cannot resolve gradients within a node, effects such as stratification have been addressed external to the code to quantify the effects on AP600 containment pressure response. The use of the relatively large lumped parameter nodes in the AP600 evaluation model also overexpands an entering jet, leading to two competing effects on containment pressure calculation - overprediction of velocity and underprediction of steam concentration above the operating deck. The competing effects have been bounded (Reference 3) by utilizing only free convection heat and mass transfer on the inside of contamment, which effectively ehmma.es the non-conservative velocity. This leaves only the underpredicted above-deck steam concentration which is itself conservative with respect to PCS heat removal.
Compasersuie CW da s were se porfered ui+h "im1=Hans "eing +he Aisukuted p-r c'^r WCO C 'erWer Se mere deuded ditibuted p:r=:ter mc&!
(Ref=:n:: L ^.ppendix " 9^r reprerert phenomer= -ere deeely m=+4er ee L9 hu,
=d he! ped cedi- & t phenc=:n: :=u--ing i- 6: LE h:d E=.- i&n9ied. 'Ih ht:i!:d dbMbuted p==: = m &! &c :cr&med oc ecmperr:9; crer !- Se ! ump ^d ;
p= metr .ede! +.!& ";;= beu-id in 6> !cping Se e>r!u2Ser m~4! r diserred abe /:. 9:=uce of prM=! compubSr !L-J+="erz, a u =r =1-+=A *e pr~wd "i& :
berdhg appread urbg 6e !"~ ped pr-e+er fem 1=+4nn af WOONC.
l Element 3 Assess Uncertainties and Develop Bounding Modeling Approaches The results of scaling, cetting, and code validation were used to establish a bounding analysis approach for each of the PIRT phenomena. Results of code validation and assessment of model uncertainties were used to develop a method of applying the MGOTHIC lumped parameter formulation to create a bounding DBA evaluation model using fixed noding.
Sensitivity calculations (Reference 5, Section 5) were performed to gain insight into the influence of important parameters on the predicted pressure response. A key aspect of the evaluation model is that phenomena that are not part of the code calculation or are not well-represented within the code are evaluated separately and bounded by applying conservative l bounda*y conditions or introducing biases into the evaluation model, as summarized in Section 2. The method used to address each phenomena in the evaluating model is documented in the PIRT (Reference 3).
Preface Revision 2 on3703wAwpt 1ts)62497
! June 1997 l
i
l l
1-5 i
The dimensionless groups needed to scale jet and plume momentum for their effects on stratification in the contamment volumes are presented and relationships between AP600
{
an,d the IST are discussed in Section 6.5. The evaluation of stratification in compartments, and circulation between compartments, on AP600 to establish a bounding approach are documented in Reference 5, Section 9.
The momentum equation for the air flow through the PCS air flow path (downcomer, riser, and clumney) are developed, made dimensionless, and normahzed to produce the pi groups required to scale momentum in the PCS air flow path.
The pi group values for the AP600 phenomena are evaluated, thereby providing a numerical basis for the,importance of the dommant phenomena (transport processes and components) and validation of the PIRT rankmgs.
Scaled data from the SETS and IETs are compared to the scaling and phenomenological equations. The scaled tests are compared to AP600 to justify the use of the tests for evaluation model validation.
The rate of change equations for the containment gas mass, energy, and pressure are derived based on simple assumptions, using thennodynamic relationships, equation of state, and control volume conservation equations. The rate of change equations represent a single gas volume that is coupled to maltiple heat sinks. The contamment volume is assumed homogenous, except for tiv: dead-ended compartments. The above-deck region is nearly homogeneous during and after blowdown due to the entramment into the plume of more .
than 10 times its volumetric flow rate. The effect on heat sink utilization of deviations from a umform vertical air / steam concentration distribution are shown to be minor (Reference $ -fe-Section 9). 5 The circulation and stratification report examines a range of break source momenta and directions, and shows that in all cases circulation between compartments mamtains all but the dead-ended compartments at, or above the homogeneous steam concentration, and the above-deck region within 2 or 3 percent of the homogeneous concentration of approximately 60 percent steam. Although containment is not perfectly uniform, the deviations from homogeneous are small enough that the conclusions of the scaling analysis are valid.
The Westinghouse containment scaling analysis has evolved through a series of issued documents, presentations, and reviews. Extensive input has been received from the USNRC and the ACRS Thermal Hydraulics Subcommittee.
Westinghouse issued Passive Contamment Cooling System Prelimmary Scaling Report, July 1994 (Reference 13) introduction Revision 2 o:\.7/03w+wpt1t42397 June 1997
21 2 DOMINANT PHENOMENA x The transport processes and components that affect contamment pressure were identified and ranked according to importance in the PIRT. The phenomena ranked high and medium are I the ones that receive more detailed treatment and validation, and should be addressed in the evaluation model. The phenomena ranked high or medium importance are listed in Table 2-1. The phenomena are organized according to whether they are represented by pi ;
groups in the scaling analysis or whether the phenomena appear as parameters in pi groups. !
Those that appear as parameters are indented in the first column of the table, and identified I as parameters in the column headed "PI Group." The high- and medium-ranked phenomena ;
evaluated in this scaling analysis are identified in the column headed "Where Addressed."
l Many low importance phenomena are also addressed in this scaling analysis. High ranked phenomena not evaluated in this scaling analysis are briefly discussed and referenced to source documents at the end of this section.
The following high ranked phenomena are addressed by separate, detailed evaluations in which AP600 parameters were ranged to derive bounding inputs for the evaluation model.
Circulation and Stratification - AP600 can be characterized by stratification within compartments and circulation between compartments. The scalmg of jets and plumes, and the relationship of large-scale test (LST) stratification data to AP600 operation is ,
presented in Section 6.5 of this document. The application of those data to AP600 is l presented in Reference 5, Section 9. The circulation rates of air and steam between interconnected gas volumes (compartments) is addressed in Reference 5, Section 9. ,
. Intercompartment Flow - The mass flow rate of air and steam between interconnected l
gas volumes (usually referred to as circulation) affects heat sink utilization and is al:o addressed in Reference 5, Section 9.
. Source Fog - Source droplets (fog) occur during blowdown and increase the steam l source density, thereby reducing its buoyancy. However, during blowdown, muang l inside contamment is momentum- and pressure-dominated, not buoyancy-dommated.
After blowdown, drops do not occur in the break source, so the post-blowdown source buoyancy is not affected. The effect of blowdown-generated drops on post-blowdown circulation is addressed in &c : i- --f _1"" "m , d However, the effect of M droplets as heat sinks is a dressed in this scahng document.
~n a .-~.a
. Liquid Film Stability - Liquid film stability affects the amount of surface area that can be covered by the PCS cooling water. In AP600, the time constant for heat transmission through the shell is relatively long, so the external surface temperature rises slowly relative to application of cooling water. Once the PCS water supply valve is opened, the water distribution weirs begin to fill and spill, leading to a development time for Dommant Phenomena Revision 2 o:\3703w-b.wptit>a2497 June 1997
1
! Table 8-3 Containment and Heat Sink Mass Scaling Pi Group Values l
Pi Group Blowdown Refill Peak Press Long Term MSLB j to(sec) 39 985 913 5173 537 Contain-ment nm., 1.31 1.27 1.30 1.22 1.27 n om 1.00 0.00* 1.00* 1.00 1.00 n ,; 1.75 0.00 2.00 0.00 0.00 Drops n 3.. 0.02 0.00 0.00 0.00 --
n ,,,, 0.03 -0.04 0.01 0.00 --
Pool n, 0.04 0.00 0.03 0.07 -
1 Steel n ,, -0.05 -1.41 -0.69 -0.02 -0.44 i Concrete n, -0.01 -0.08 -0.02 -0.09 -0.12 Jacketed n, -0.02 -0.46 -0.23 -0.18 -0.08 l
Sc Shell n, -- -
-0.01 -0.% -
)
Evap n,m
-0.43 -0.90 -
i Shell l
,_ n ,,, - -
-0.02 -0.89 -
l l
Dry Shell n m .o, -0.02 -0.61 -0.03 -0.08 -0.37 l
Baffle n, 0.00 0.00 0.00 0.00 - I Chimney n,m 0.00 0.00 0.00 0.05 -
l l
- Refill was scaled with the same 200 lbm/see flow rate used to normalize peak pressure. I i
%e/
^
1 l
l Table 8-4 Containment and Heat Sink Energy Scaling Pi Group Values Pi Group Blowdown Refill Peak Press Long Term MSLB Contain- n,, 0.55 0.58 0.56 0.63 0.58 n, m 1.00 0.00* 1.00* 1.00 1.00 n,., ,m 0.00 0.00 0.00 0.00 0.00 Drops n, ,,, 0.00 0.00 0.00 0.00 --
3,3,, 0.05 -0.04 0.00 0.00 -
Pool n,y , 0.00 0.00 0.00 0.00 -
n,u, 0.03 0.00 0.02 0.06 -
Steel n,y,, 0.00 -0.08 -0.03 0.00 -0.03 n,3,, -0.05 -1.35 -0.64 - 0.02 -0.44 n ,,, 0.00 -0.05 -0.05 0.00 -001 Concrete n ,, 0.00 0.00 0.00 0.00 -0.01 n,3, -0.01 -0.07 -0.02 -0.08 -0.12 n ,, 0.00 -0.01 0.00 -0.01 0.00 Jacketed n,y , 0.00 -0.03 -0.01 0.00 -0.01 Concrete n,3, 0.02 -0.44 -0.21 -0.16 -0.07 n,,, 0.00 -0.02 -0.02 -0.02 0.00 Subcool- n ., - - 0.00 0.00 -
ed Shell n 3, -- -
-0.01 -0.06 -
n,;, - - 0.00 -0.01 -
n .... - - -0.01 -0.08 --
Evaporat- n,,,, - -
-0.02 -0.03 --
l ing Shell n,a,, -- - -0.41 -0.81 -
j K.;,. -- --
-0.02 -0.09 --
n,y,. - -- 0.00 -0.03 --
n,a,o - -
-0.02 -0.81 --
Dry Shell n,yo 0.00 -0.03 0.00 0.00 -0.02 l n, ,,.,, -0.02 -0.59 -0.03 -0.07 -0.36 n,;. 0.00 -0.02 0.00 -0.01 0.00 n, ,, 0 00 0.00 0.00 -0.03 --
Refill was scaled with the same pressure normalization used for peak pressure.
J s
Table 8-4 Containment and Heat Sink Pressure Scaling Pi Group Values (cont.)
Pi Group Blowdown Refill Peak Press Long Term MSLB Chimney n, 0.00 0.00 0.00 0.00 -
n,,,, 0.00 0.00 0.00 -0.05 -
n,a 0.00 0.00 0.00 0.00 --
Baffle n,yu 0.00 0.00 0.00 -0.02 -
n, , 3,, 0.00 0.00 0.00 -0.02 --
Refill was scaled with the same pressure normalization used for peak pressure.
i i
4 J
w
_~ _ _
~'
Table 8-5 Containment and Heat Sink Pressure Scaling Pi Group Values Pi Group Blowdown Refill Peak Press Long Term MSLB i l
Contain- n,., 0.76 0.76 0.77 0.76 0.76 )
ment ng, 3,, ,,,, 1.00 0.00* 1.00* 1.00 1.00 n,,,,,,. 0.03 0.00 0.03 0.02 0.03 n g6 0.00 0.00 0.00 0.00 0.00 Drops n,.,.4 0.00 0.00 0.00 0.00 --
n g ,..a 0.00 0.00 0.00 0.00 --
n,...,ia 0.05 -0.04 0.01 0.00 --
Pool n,,, 0.00 0.00 0.00 0.00 --
n,, . , 0.00 0.00 0.00 0.00 -
n, .o,, , 0.04 0.00 0.03 0.07 -
Steel n, ,,, -0.01 -0.24 -0.09 -0.00 -0,09 n,, ., 0.00 0.00 0.00 0.00 0.00 n,..i, -0.05 -1.41 -0.69 -0.02 -0.44 Concrete n,,, 0.00 -0.01 0.00 -0.01 -0.02 n , ,,,,, 0.00 0.00 0.00 0.00 0.00 n,. 6 , -0.01 -0.08 l -0.02 -0.09 -0.12 Jacketed n ,., , 0.00 -0.08 -0.03 -0.01 -0.02 Concrete n ,,,, , 0.00 0.00 0.00 0.00 0.00 n, , -0.02 0.46 -0.23 -0.18 -0.08 Evaporat- n,4,, - -
-0.07 -0.08 -
ing Shell
_n,,... -- - 0.00 0.00 --
n,. .
-0.43 -0.90 -
Subcool- n,, - -
0.00 0.01 -
ed Shell n,,.. - -
0.00 0.00 --
n, . ,. . - - -0.01 -0.06 --
l Dry n,,3, 0.00 -0.10 -0.01 -0.01 -0.07 l Shell l n,, .. 0.00 0.00 0.00 0.00 0.00 n,... . -0.02 -0.61 -0.03 -0.08 -0.37 Refill was scaled with the same pressure normahzation used for peak pressure.
l
10-5 where the length parameter is the annulus hydraulic diameter, h d . Incropera and DeWitt (Reference 32), Table 8.4, suggest the use of Colburn, Dittus-Boelter, and Seider-Tate v' correlations for intemal flows.
4he.
The Dittus-Boelter correlation differs from Colburn by a Prandtl number exponent of 0.4
$ instead of 1/3. For the predommantly air flows in the PCS, Dittus-Boelter g&;c mde less than Colburn. " ^
that are 2 percent,ger coer takt n grehe.\5 hed kansfer coehenks The Seider-Tate correlation adds a multiplier of (p/p[14 to the Colburn correlation.
4 For the PCS with air and bulk-togurfac Tatep ;;i= ~de 2 percent Iselb,e temperature differences less than 100*F,,Seider-Colburn. W )
cors* Mien. Feedicts heak 4cansiu c <heaks Wak are All of these correlations are recommended for Re > 10,000, L/D > 10, and .7 < Pr < 160. The corresponding AP600 parameters are 16,100 < Re < 163,000, L/D = 60, and Pr = 0.72 which
- satisfy the criteria for use cf the Colburn correlation.
10.1.4 PCS Air Flow Path Flow Resistance The natural circulation air flow rate in the PCS air flow path determines the riser Reynolds 4
number, an important parameter in the evaporation mass transfer correlation. The PCS flow resistance is one of the dommant terms in the PCS mornentum equation presented in -
Section 9. He form loss coefficient measurements from a geometrically scaled model of the AP600 PCS air flow path are presented and extrapolaMd to AP600.
The flow resistance in the PCS air flow path was measured in the 1/6 scale air flow test l
(Reference 31). Although AP600 operates in natural circulation and the test was fan forced, !
the buoyant pressure,o G , and the forced pressure drop, AP, are interchangeable in the pi !
groups. Consequently, a fan forced test produces a flow resistance that is equally valid for a I buoyancy driven system.
)
i ne overall pressure loss coefficient for the system is a combination of form losses and friction losses. It is known from the test that the form and friction losses are approximately I equal. Thus it is expected that the resistance should be a weak function of the Reynolds number, with an exponent on the Reynolds number approximately one-half the Reynolds number exponent for pure friction at the same Reynolds number. This can be demonstrated as follows.
Since form losses are known to be independent of Reynolds number at high Reynolds 0
numbers (K = C iRe ), and since the frictional losses are known to have only a weak dependence on Reynolds number at high Reynolds numbers (fL/d = C2 Ren , where n = -020),
it is reasonable to expect the sum of the form and friction losses can also be approxunated by
- a function of the form K, = C Re". 3 An approximating function can be deSned as the Evaluation of Scaled Tests Revision 2 onmnw-d.wyt !b.062597 June 1997
~
11-6 No Circulation Below-Deck - The lack of an opening between the simulated steam generator compartment and the other below-deck compartment that was open to the above-deck region
, prevented the above/below-deck circulation that would otherwise have developed. It also caused air-rich mixture below-deck and a steam-rich atmosphere above-deck. This, combined with other differences that affected heat sink effectiveness resulted in a distortion in the scaled transient pressure response in the LST. Consequently, circulation is a system level distortion.
The parameters that affect the mass transfer rate were measured and accounted for as pararneters in the mass transfer correlation. Since the resulting range of independent variables in the test covered the range in AP600, as shown in fection 10.1, there is no 3'
distortion in the use of the LST as separate effects datt. The LST data were further supplemented with data from intemational test at various larger scales to support the definition of a bounding approach for modeling the effects of internal circulation and stratification.
External Water Flow too High 'Ihe energy and pressure scaling pi groups for the subcooled g shell presented in Tables 8-4,8-5, andg I show subcooled heat transfer effects are second-order phenomena. Consequently any difference.s between the test and AP600 values have only a minor effect on the system presure response and thus are not system-level distortions.
3
.. The results of scahng test 213.1C presented in Table Mshow the measured value of n,,q,,x T is less than the calculated value for AP600. Consequently, the amount of heat removed by the subcooled liquid in the LST is not always greater than in AP600. There are, of course other tests with higher extemal water flow rates in which the IST scaled heat removal is 4
greate'r than that in AP600. Since the flow rates were not all too high, the effect is that of a ranged parameter, and is neither a difference nor a distortion.
External Water Flow Was Established Before Break - The extemal water flow is one of several external processes that combined to produce the rate of heat removal from the contamment gas. Sixe the system level pressure and scaled dominant variables are distorted, it is likely ' hat the extemal water flew contributed to the distortion.
Two tests were conducted that had cold water applied to a hot shell. LST 219.1 operated at a dry steady state shell temperature of 240 F, then water was applied. One shakedown test was operated at 250 F shell temperature, then water was applied while the process was video taped. These tests provided separate effects test data and behavior to support the validation of the extemal wetting and stability model.
Distortions and Uses for the IST Revision 2 oA3703w d.wphlb-062397 June 1997
Table 21 Phenomena identification and Ranking Table - Summary of High and Medium Ranked Phenomena Phenomenon
- Effect on Containment Pi Groups Where Addressed Break Source Mass and The only mass and energy source xp.g.brk.d Scaling Analysis
, g Enerev (1A) for containment pressunzation up.g.brk work Q.;dt; : ._) and x p. work.a Evaporanon (58) x p. work.,
i Gas Compliance (2C) Stores mass and energy in xp,, Scahng Analysis 1
atmosphere, increasing pressure i
Initial Conditions inside Temperature, humidity, pressure None Initial Conditions (4A, 4B, 4Q affect noncondensables and energy Ref. 5, Section 5 storage Contamment Solid Heat Sinks (3), Pool (S), Drops Store energy (and remove mass from atmosphere) reducing F[
xp Scahng Analysis -)E I
(1), and Shell (7) pressure
- 1 Internal Heat Sink Limits conduction heat transfer parameter Scahng Analysis Conduction (31% into heat sinks, shell, or pool, and SE,75!)and Heat through shell. Stratification in the l j Cap (EE, Sg break pool can affect the effective heat capacity of the pool l
s
) ;
- - Heat Transfer Water and noncondensible layers parameter Scahng Analysis Through Horizontal on upward facing horizontal .
1 Liquid Films W surfaces limit heat and mass '
I transfer to horizontal heat sink Condensation Mass The single first-order transport xp,,,,g,j Ecaling Analysis i Transfer (WcfBb p process that removes mass and energy from the contamment gas Break Source Direction, elevation, density, and parameter Circulation and Direction and momentum can dommate Stratification,
, Elevation W circulation and affect condensation Ref. 5, Section 9
- Momentum ( rate. Existence of droplets in Density source during blowdown affects f- p ' s.L7 the effective source density.
i Circulation and Intercompartment Flow Stratification M (Circulation) and stratification can affect the distribution of steam parameters l Interco artment near heat sinks for condensation Flow heat removal. Pli.; 'J62 !=d C ,e <
] th & E..a i .i t;n ";.
$# b$5b[b. 8 )N Source Fog @ Affects circulation and parameter stratification via buoyancy i
1 Dommant Phenomena Revision 2 on3m3we wptit>.062497 June 1997
2-4
)
Table 2-1 Phenomena IdentiScation and Ranking Table Summary of High and Medium Ranked (cont.) Phenomena Phenomenon
- Effect on Containment Pi Groups Where Addressed Evaporation Mass The first-order transport process n,4., Scahng Analysis Transfer M that removes mass and energy i from the evaporating external shell l PCS Natural Convective air flow provides parameter Scahng Analysis Circulation M convective heat and mass transfer i M) from contamment shell.
Liquid Film Flow Affects the upper limit for water parameter F;1m Stability, Rate hWat r coverage on the external shell Ref. 5, Section 7 .
Temperature ,
l Film Stability G i
Liquid F e inside-h Transport Carries 14 percent of condensatien energy to the IRWST and break x,j Scaling Analysis pool. See note 1 Outside:
Absorbs 8 percent of energy Ye,p ssy.
rejected by the external shell
, surface.
C . Heat Transfer A second order transport process xp43 T (38 ,S that removes energy from the x,4 ,+x,4 Scaling Analysis 14A) contamment gas, and from the asx extemal shell. Note 2 Ra cat Transfer A second order tr sport process xp4; Scaling Analysis that removes energy from the x,4 ,+x,4 Contamment gas and from the an external shell. Note 2 Baffle Conduction $. Conduction through the baffle into se4 bt, PIRT Sections and Baffle leakage paths downcomer volume and leakage n 4.4.10D and e4 bfx 306) paths can influence the external None for 4.4.10G natural circulation flow rates leakage Indicators in parentheses refer to phenomena in the " Phenomena Identification and Rankmg According to Effect on Contamment Pressure" (Reference 3, Table 4-1).
Note 1. W fraction of the internal condensation energy carried away by the liquid film is defined by the ratio: x,j3 /(x,jpx,g3), for each heat sink J. The fraction of the external shell heat rejection that goes into the subcooled heat capacity of the extemal liquid is defined by the ratio: x,4 , /(x,43,,+
x,4 ,+x,4 ,+x e4 dsx). The pi group values for AP600 are presented in Section 8 p represents the pressure effect of satsible heat transfer. W sensible Note 2. Inside contamment x h2 radiation heat transfer and 1/2 conv heat transfer is approximately . Outside contamment x,4 ,+x,44, represents the sum of the dry and evaporating shell sensible heat transfer, that is approximately 1/2 radiation heat transh:r and 1/2 convection heat transfer.
~
Dommant Phenomena Revision 2 o:Wo3wAwpf 1b.062397 June 1997
- 2. (RAI 480.995) In the previous revision of the scaling report, the Biot number had been calculated to be 0.08. Now it has been recalculated as 0,13. According to Kreith, *Pnnciples of Heat Transfer," 3rd ed.,
p.140,'a enterion for treating a heat structure as a lumped mass is that the Biot number be less than 0.1.
/ Since Kreith's criteria is no longer satisfied, what is the justification for lumping the steel? What is the l magnitude of the error introduced by this approximation?
l I
RESPONSE
Kreith's Biot criteria Bi < 0.1 is based on a temperature error of less than 5%. It is estimated that Bi <
0.13 would give a temperature error ofless than 10%. Such an en.. is considered acceptable for a scaling analysis in view of the simplicity of the lumped parameter assumption.
To clanfy the use of Biot numbers Bi < 0.13, the first paragraph of Section 7.5.5," Steel Thermal Model,"
WCAP 14845, Rev. 2," Scaling Analysis for AP600 Containment Pressure Dunng Design Basis Accidents,"
l will be deleted and replaced with the following:
l l "The average steel thickness, calculated from the steel volume / area (Section 3) is 0.4 inches. The Biot number for steel of the average thickness is Bi = 0.13.
From Kreith's text (Ref. 20), a Biot number of Bi = 0.1 is noted to result in a maximum temperature error of no more than 5%. It is estimated that a Biot number of Bi < 013 will result in a maximum temperature error of no more than 10%. Such an error is considered acceptable for a scaling analysis in view of the simplicity of the lumped parameter assumption. Thus, the steel can be modeled as a lumped mass and T,,, = T in Equation (118). With this assumption, the surface heat flux and total stored energy in the heat sink can be related to the heat sink surface temperature and average temperature.'
l s 1
)
1
=
~
l
! .uc . . . 2 l
l' 1
i ,. -
- _. _ ,. ~,_ -
7-29 )
i i
i and the external film outer surface with convection heat transfer and evaporation to the riser bulk flow, and radiation to the baffle is: ,
s xf.s -Tbf T ,3xf -T n = ("
ut hmx +hcx+h y(Txf,3 -T n (132)
These two equations are added, resulting in the equation:
I
. 1
.u! '
h mx +h cx Tg3 -Tbf) " (133) l (Tsho -Tri)
- 9ounSV).3 +
+h,x((T
, , xf,,-T ri) , , ;
The term in brackets is the inverse conductance for the outside of the shell, where the l
conductance is h,x,o. Equations (130) and (133) can be combined with the general energy equation for a heat sink, Equation (90), to give:
dT m sh Cv,sh h, A (T -Tsh.i) - h,x A(Tsh,o -Tri) dt
~
Equation (134) was written for the evaporating por' ion of the shell, but is also valid for the subcooled and dry portions of th external shell, with substitutions for the subcooled region hmx = hex = rx h = 0, and for the dry >ortion hy=hmx = 0.
The areas of the subcooled and evaporating regions can vary with time, so a basis for calculation is required. The area of se subcooled region is determined from an energy balance on the subcooled liquid in which the heat conducted from the shell heats the liquid from its source temperature to the temperature of the evaporating film, Tg. The subcooled film is assumed to have no evaporazon, radiation, or convection from its surface. The bases for this assumption are:
The subcooled water exists at :ne top of the shell where the riser temperature is at its maximum. When compared to de average subcooled film temperature, TM avs =in(T +
Tg)/2, the difference (T xf,,yg. T.g is a small positive value at peak pressure, and a small negative difference at long-te:= pressurization.
The subcooled surface area is relatively small, only a few percent of the total, so errors l have little effect on the evaocrz:ng region where most of the shell heat is removed.
The calculation proceeds by calcula= z the temperature of the evaporating film, Tj ,3, as shown in Figure 7-3. The water ilev. ng over the subcoo;ed shell surface area,4 gg assumed to heat linearly from the e' . source temperature, T g
in to T g ,3 The average subcooled film temperature is then 7 ,g = (Tm+Tg3)/2. A simple energy balance on the l
l Heat Sink Analysts and Equations ict b tg Revision 2 l on3703w+wpt:1b42397 June 1997
7* '
49 '
subcooled film can be written relating the sensible tempera e rise of the ftim to the energy conducted into the film from the shell. That is, rha c y(T , - Tin) = h 4 sc xfavs - T The subcooled film conductance is defined in Equation (142). The su le film area is y l estimated by rearranging this energy balance.
ssY. I s
rhxfcy(Txf T) p in (U,5) gSSX= h xfgT,,x -T xfevg I f Ssx ssx The liquid fthn we ed surface area is then estimated as discussed in Section 7.6.6, and the evaporating area - the difference between the wet area and the subcooled area, l
- g. A,y,p = Awe- The dry area is the difference between the total area and the wet area, Adry = 52662 ft.2 -A w ,.
7.6.1 Shell Conductance '
I The individual conductance terms inside the shell are free convection heat and mass transfer, radiation, and liquid film conduction. These are evaluated independently for the internal !
portions of the shell that correspond to the subcooled, evaporating, and dry portions of the external shell.
0.13(h g -h f )p3,D y AP,, r3p ,1/3 N= Pg ,,p k
(T-TU)(V /8)1/3 ,
0.13 k 'op 'l/3 )
h= Pr ,
2 (v jg)1/3 , p s (136) l h, = or f(T,Tu) hg = kg /Su h, = [(h, +h e+h,)~l + h[]-1 1
4 Heat Sink Anaiysts and Equations for Scahng Revision 2 o:\3703wkwpt:1N7
}une 1997
7-31 l
' The conductance pi groups are each of these values divided by the reference shell conductance for each of the three shell portions. The fifteen pi groups result:
h,,,c,, h m,3c,o he,3c,o b r,se,o K ~ ~ h ux,o c.ex " hsh ,o *
- 5' h sh.o *
h sh ,o C'*
'd*
h sh,o h sh ,o l
l Ac,e.es " Ac.m,es "
A c,c.es " '
Kc.r,es " Kc,if,e3 = '
h e,ds.o N,ds,o h e,ds,o h r.ds,o Ac ,e,ds " c,m,ds " c,c,ds " h u,ds.o h sh,o hsh,o hsh,o c,r,ds " c,if,ds "
h sh,o h sh,o (137)
The evaporating portion of the sheL outside operates with forced convection heat and mass transfer, radiation, and liquid film conductance:
h, =
fgse P S #se m,esx (T -Txg)dh P gi, ReIsgcif3 g l
hee 0.0 m g as
=
,d Pr '3 l
l dh c.,e 5x (138) h, = oc f(Tg ,T bf ) h4 = kg /6 g f, ew. xtesy.
rO -1 h,x = h mx +h ex +h,x Tu-Tbf) ' 'l
,k
((T -Tn)
+ he-1 b
Xf Heat Sink Analysts and Equations for Scaling I o:\3703w-b wpf.lb 062397 Revision 2 June 1997
7-41 m
The method used to calculated the evaporating, subcooled and dry areas ts:
- Calculate the subcooled area as described in Section 7.6 and Equation (135).
- Subtract the subcooled area from the maximum wet area (44,5962 ft - Q to get the y maximum evaporatirig area. 54
= Use the maximum evaporating area to calculate the total evaporation. If the total evaporation is greater than 40 lbm/sec (Reference 5, Table 7-9, peak heat flux) then reduce the evaporating area until the evaporation rate is 40 lbm/sec.
= Subtract the evaporating area and the subcooled area from the total area to get the dry 2
area Adry = 52,662 ft - Au - A,y,p. g 7.7 BAFFLE ANALYSIS AND SCALING EQUATIONS The baffle receives heat by radiation from the shell and loses heat by radiation to the shield building and by convection to the riser and downcomer. The energy equation for the baffle is formulated accordingly, assummg radiation heat transfer from both wet and dry portions of the shell that are generally at different temperatures. Exammation of when the shell
- becomes wetted, and the temperatures calculated for the wet and dry portions of the shell shows that through the beguuung of the peak pressure time phase, the outer shell temperatures for wet and dry portions are sufficiently close in temperature that wet or dry does not matter. Furthemsore, once wetting is well along, the shell heat rejection to the baffle can be muumtzed by assummg 100 percent of the shell is wet (although for shell evaporative heat losses to the riser a lesser fraction is assumed wet). For the scaling analysis the baffle was forced by the dry shell during blowdown and refill, and by the wet shell from the beginning of the peak pressure period and beyond.
The baffle is a thin steel member with a Biot number, based on the inside surface maximum 2
dry heat transfer coefficient of 11 B/hr-ft -F, of 0.0044. Even with condensation h is 2
approximately 100 B/hr ft -F and Bi = 0.04. Both of these values are small enough that the baffle is well represented as a lumped mass with identical bulk and surface temperatures. l Both sides of the baffle are subject to forced convecdon and radiation. The downcomer side l of the baffle is always dry. The riser side of the baffle may be wet or dry, depending upon the radiation heat transfer rate to the baffle and the convection heat transfer from the baffle to the riser and downcomer. The energy equation for the baffle is:
i m.
Heat sink Analysis and Eg sations for Scaling Revtsion 2 o:\3703wAwphib42397 June 1997
7-42 dTbf mbfv g C = h,,gg, A(T,g -Tbf) + hej
_/
3 +f A(Tn -Tbf) - h r.b'aeA(T bf -Tde)
(156)
- he ,bfecA bf U -Tde) + 5 h stm.bf fs in terms of inside and outside equivalent conductances, the baffle equation is:
dTbf m bfCv g = h, Abf(Tn -Tbf) - hex^bf(Tbf -Tde) 7.7.1 Baffle Conductance The individual baffle conductance terms are:
h,,g4f = oE f(T,g,Tbf) hr .bf ac = OEf(T bt ,Tde)
, hisAsnDy@stm
^
0.023 Red' SC dri -Tbf)dhPgj, 1
(158) hejag = l 0.023 Red' Pr /3 h e.bf-dc = 0.023RedloPr[3 (T,g -Tb')
h, = h m,n g, +he,n +f +h y ,g4f h,x = h ,bt-dc e +h r.bf-de 1
@ p a +he dow 4e df cms.skeM WA 4h' "'"u' **
__' ' i Bckh be riser (operaty[tn forced convection [aM 0.dn.mu.m b oyyom; mmJ wumaen.
The liquid film conductance on the baffle is neglected.
The individual conductance terms are normalized to the shell condt ctance, h ,o , to produce sh the pi groups for scaling the heat sutk conductances:
Heat Sink Analysts and Equations for Scaling Revision 2 o:\3703w4 w41397 June 1997
. . ~. . . - - . . . - - . _ - _ - - _ . _ _ _ - _ - - . _ . _. - . --. .
l S. (RAI 480.1017) The RAI was directed toward determining whether any of the remaining pi group values contained an anomaly similar to that for pi, The NRC review did not check the value of every pi group.
Please provide an evaluation of the anomaly effect for pi o and pi m. ;
7 \
> w
RESPONSE
l l Note: Previously, a response to this question was prepared that included two paragraphs l followed by a table, followed by another sentence in bold letters. The complete response to this itim keeps the first two paragraphs and the table, titled " Table 1 -- Temperature Differences and Heat Transfet Coefficients for the Shell and Bafne.' The following text
- is to be inserted immediately following Table 1 of the previous response.
l Insert after " Table 1 Temperature Differences and Heat Transfer Coef5cients for the Shell and Bafne."
Westinghouse will delete the last paragraph in Section 8.2, " Conductance P! Group Values," of WCAP.
14845, Revision 2," Scaling Analysis for AP600 Containment Pressure During Design Basis Accidents,"
and replace it with the following text.
The remaining conductances range from 0.01 to 0.05. These are small values.
mainly because mass transfer is not involved with the energy transport associated in these regions. The chimney operates with low conductances, even when condensate forms, due to the high non-condensible concentration in the adjacent air Dow. The dry shell external conductance is I to 2 orders of magnitude less j than the internal conductance associated with the internal shell.
The outside and inside befue surfaces both operate dry and, consequently, have low conductances. The low values are indicative of the small energy transport ,
associated with these surfaces. Furthermore, the energy transport processes I across the two surfaces are similar in magnitude and should have similar l conductance ratios for all time periods during transient. The negative conductance ratio calculated for bafne inside surface during the long term portion of the transient is the result of an unfortunate selection in temperature difference for normalizing the conductance. This negative value is not ;
meaningful for comparison purposes and should be ignored.
l l
. . . . 3
. - - . - - - _ - . . . . - - - - . _ - - - - _ . . - .~... _ ... . _ - , - . . _ _ - ... -
7, (RAI 480.1027) In addition to the information in the RAI, the following is needed to complete the review.
Please compare the physical film thickness (as predicted by the Nusselt equation) to the Chun and Seban s
effective film thickness over the range of Reynolds Numbers expected for the AP600 (both inside and
,) outside the PCS, above and below the second weit). For each Reynolds Number, compare the heat transfer coefficient for the water film using the Nusselt model and the Chun and Seban model.
The _ wording in the first paragraph of Section 7.4 has been improved to distinguish the effective film
. thickness from the physical film thickness. Unfortunately, in the second paragraph, the effective film thickness is used to get the heat capacity of the film, whereas the physical thickness should be used. The difference in the ratio calculated is not significant, but it confuses the issue,in the sense that it encourages the reader to thmg of the effective thickness as a physical distance.
RESPONSE
First two paragraphs of existing response as good as is.
The condensation heat transfer data of Kutateladze et.al. for working fluids of refrigerant 12 (Pr = 3.5) and refrigerant 21 (Pr = 3 06) is added to the graph given in Figure 3.101. This amended figure is attached.
. Also, the following text will be added to the text of section 3.10, "Chun and Seban Liquid Film Conductance Model," of WCAP 14326, Revision 1:
. See marked up page that is attached.
Insert 3: Kutateladze et. al. determined the heat transfer coefficients for two working fluids in film condensation on vertical surfacesM These two sets of data are also plotted on Figure 3.101 and are nominally identified as having Prandtl numbers of 3.06 (actual range of
- 2.74 to 3.06) and 3.5 (actual range 3.14 to 3.52). At lower Reynolds numbers, Re < 100,
. the Chun and Seben correlation provides an upper bound to data for both working fluids.
- Between the range of 100 < Re < 400, the Chun and Seban correlation provides a "best estimate' fit to the data. In the range of 400 < Re < 2000, Nusselt numbers given by the Chun and Seban Wavy Laminar Correlation are lower than (conservative relative to) the data reported in Reference 25.
, - Insert .4: Using the AP600 containment Evaluation Model's minimum liquid film flow rate ofIb
= 120, a minimum evaporating film Reynolds number of about 700 is calculated.
Comparing the Chun and Seban correlation to the data above this Reynolds number, the correlation is observed to be : good fit to the evaporation data and conservative relative to the condensation (lower than the data).
Also, the list of references will be amended to include the following; REFERENCES
- 25. Kutateladze, S. S , Gogonin, I. !.. Origo'eva, N.1. and Dorokhov, A. R. " Determination of Heat Transfer coefficient with Film Ccndensation of Stationary Vapour on a Vertical Surface,' The: mal Engineering, Volume 24, Number 4, pp 184186 (1980)
I l-l
[ .
s .-
. ... . 4 I
g T& Ckdk cerrele}rk as d 4 $ L 4.~f W M lvr-*o p $ b b 4k fw- mde Liquid 3,10 Chun and Seb LG Film conduc e Modelm g
] MF 3. ip-t sed to predict h
' (1 5 tran er through the condensing and 7
h h he Chun and S grrelatio evaporating liquid filmsA R : _ . - ..;.pp'in :a b tbulent and wavy laminar films,xd ec=
cemp J iv J ; in and de r .'!6; f i; Ch- - J e . .pgrg g;..yg. :=ptbe
.cL ;; ::gcondensing Universgfgisconsin33) wavy laminar 0:; =d :: surfaces that are :
incline ew the dome region of AP600.
(p,1.1.,45',a.d88 Y&
Ac Erim Nf ne Wisconsin test facility is described in Section 3.8. Five of the Wisconsin (23) tests (95 through 99)
@( were conducted without a noncondensible gas present. Without a noncondensible gas, the gas-to-( liquid heat transfer coefficient is so high that the gas-to-liquid temperature drop is negligible compared
) to the temperature drop across the liquid film. Consequently, the temperature of the liquid film
( surface may be assumed equal to the gas temperature and the liquid film hear transfer coefficient can be calculated from the heat flux divided by the liquid film temperature drop. Since the heat flux, solid surface temperature, and liquid film surface temperature are known, the heat tramfer coefficient may
}
be derived directly from the measurements. He Wisconsin tests thus provided a direct indication of the liquid film hear transfer coefficient for a rang'e of surface inclinations from vertical to horizontal, (covering a range of film Reynolds number in the wavy laminar regime.
3: "*c=&" mu Cwu ad 'h.L;.a* ' ^^? :.;; ;;;p A w Gm Gmu =>d Schai k m. c.ed
=;t : ;er;;'de: ' FW; : 3.104. Tuo w..Jr.;ien y.d cu r_h ta;,.am , Jm.. v c4 me M 't.go;d immuci . p vf ' - ne range of film Reynolds numbers on the outside of AP600 is .
also shown in the re f 11 withm the range of the test data. Reynolds numbers on the inside of containmen p .,;; .r. oukide due toOn .g r iS ~~ M M s@r .wg tokbYWY[Tih flows dowr
' "$NSYs AP600 WNN'*$?e liquid filtR Pran~dtl n[nberW!dNh ge is approximate ran&NV!<[.5 whereas < Pr < 3
- the range of the Ekm data Prandtl numbers is 1.77 < Pr < 5.9, which adequately covers the AP600 range. Comparison of the correlation to the test data show that the Chun and Seban correlation is a good, best-estimate representation of the data.
The large scatter in the Wisconsin (23) 1iquid film heat transfer data is believed to result from operating W h the tests at (or beyond) the range of operation for which the test facility was designed. De presence of even small amounts of noncondensible gases would bias the results.
i o-\3s42w-4 *PtitM)S0597 Rmston 1 3-7 [ May 1997
1
\
1 1 0.9 - -
0.9 0.8 - Chun and Seban Turbulent Correlation
-Chun and Seban wavy Nu = 0.0038(Re) #(Pr) "
0.7 -
- 0.7 Laminar Ch 0.6 -
Nu = 0.822(Re)#** Pr = 5.1 Z
(9 0.5 k Pr = 5.7 Pr = 2.91 0.5 y . *
- c +
Z s 0.4 ..4 ,,-
==. f_ -
0.4 ;
r * .* *4 f (9 . - *' '
"
- I ~E."f. - d
- fl* " " ;" " "
~
$ o.3 -
0.3 Z
Pr = 1.77 g g . ,-
$.. * .. o,.
g -
g .
N
- 0.2 0.2
.sr
.J -
s
\
9 +
AP600 Range (from second weir) i i 1
0.1 i i i ' ' ' ' ' ' ' ' ' ' ' O.1 i i i i iiiil i
'l l 10 100 1000 10000 100000 Liquid Film Reynolds Number, Re Wsconsan Chun & Seban Chun & Seban Chun & Seban Chun & Seban Kutateladze Kutateladze Pr = 1.77 Pr = 5.7 Pr = 5.1 Pr = 2.9 Pr = 1.77 Pr = 3.06 Pr = 3.5 4 o D + % * =
.-. ~ ... - . .~ -. - - - - _ - _ - .. . - - .... - - . - _ - . - . - . - . -
- 8. (RAI 480.1031) In Table 10 3 the new footnote reveals that for LST, measured air / steam concentrations were used since LST is not homogeneous. How were the air steam concentrations for AP-600 determmed for use in calculating the pi-group?
j
RESPONSE
Five cases of the rising plume from the break mixing with containment atmosphere were evaluated in Section 9 C.I.4. For the case of the weak (minimal entrainment) plume the variation in relative steam concentration from top to bottom along the vertical contamment shell is calculated to be no more than 0.073. Thus, for practical purposes, model predicts the containment atmosphere maintains a relatively uniform steam concentration.
Section 1.2 of WCAP 14845, Revision 2, " Scaling Analysis for AP600 Containmer.t Pressure During Design Basis Accidents states the well-mixed tir/ steam containment atmosphere is assumed. To provide a basis for this assumption, page 15 of Section 1.2, WC AP 14045, Revision I, will be amended as shown in the attached mark-up to reference Section 9.C.I.4 of WCAP 14407, Revision 1,"WGOTHIC Application to AP600."
l The following will be appended as footnote (4) to the column labeled "AP00" in Table 10-3 of WCAP. i 14845, Revision 2, " Scaling Analysis for AP600 Containment Pressure During Design Basis Accidents;"
(4) Predicted using umform air / steam concentrations a4 stated in Section 12, page 1-5 of this report. l l
h l !
1 I
i l
l i
l l
i i
f i.
1
+
l'
. . . " 5
. 1-5 l
The dimensionless groups needed to scale jet and plume momentum for their +
ffeq ts on stratification in the containment volumes are presented and relationships betweWAP600 t
and the LST are discussed in Section 6.5. The evaluation of stratification in compartments, l and circulation between compartments, on AP600 to establish a bounding approach are documented in Reference 5, Section 9.
He momentum equation for the air flow through the PCS air flow path (downcomer, riser, and chimney) cre developed, made dimensionless, and normahzed to produce the pi groups required to scale momentum in the PCS air flow path.
l The pi group values for the AP600 phenomena are evaluated, thereby providing a numerical basis for the importance of the dominant phenomena (transport processes and components) and validation of the PIRT rankings.
Scaled data from the SETS and IETs are compared to the scaling and phenomenological j equations. The scaled tests are compared to AP600 to justify the use of the tests for '
' evaluation model validation.
The rate of change equations for the containment gas mass, energy, and pressure are derived based on simple assumptions, using thermodynamic relationships, equation of state, and control volume conservation equations. The rate of change equations represent a single gas volume that is coupled to multiple heat sinks. De containment volume is assumed homogenous, except for the dead ended compartments. The above-deck region is nearly homogeneous during and after blowdown due to the entrainment into the plume of more than 10 tunes its volumetric flow rate. The effect on heat sink utilization of deviations from a l uniform vertical air / steam concentration distribution are shown to be minor Section 9).
The circulation and stratification report exanunes a range of break source momenta and directions, and shows that in all cases arculation between compartments maintains all but the dead ended compartments at, or above the homogeneous steam concentration, and the above-deck region within 2 or 3 percent of the homogeneous concentration of approximately 60 percent steam. Although contamment is not psicctly uniform, the deviations from.
homogeneous are small enough that the conclusions of the scaling analysis are valid.
The Westinghouse containment scaling analysis has evolved through a series of issued documents, presentations, and reviews. Extensive input has been received from the USNRC and the ACRS Thermal Hydraulics Subcommittee.
Westinghouse issued Passive Contamment Cooling System Prehmmary Scaling Report, July 1994 (Reference 13)
Introduction Revision 2 a:\3703w4wpt itanr1 June 1997
11-7 Intemal Heat Sinks Not Prototvoic - The scaling analysis shows the net heat sink l performance in the LST is not distorted during the early portion of a blowdown or during )
s steady-st;te operation, but is distorted between these times. J Condensation and heat transfer to the shell were characterized using detailed local measurements in a separate effects mode. The different internal heat sinks in the I.ST did not affect the validity of the condensation separate effects data.
External Water Flow Time Variations - The extemal water supply rate varied with time. The flow rate dropped when the boiler feed-water level initiated refill of the feedwater tank, i temporarily reducing the extemal water flow rate. The cycling rate was proportional to the I steam flow rate, and was typically on the order of a few minutes. The reduced flow portion l of the gcle was only a fraction of the total cycle, with the majority of the cycle operating at the set flow rate. The flow cycling may have had a minor effect on the vessel cooling and j water coverage. Since all but two tests operated with significantly more flow than could evaporate, the flow fluctuations had little effect on cooling. Consequently, the extemal water flow variation is not a distortion.
The separate effects test data used to validate the heat and mass transfer models used time and spatial-averaged temperamres, flow rates, and fluxes. The averaging time period was long enough to include several cycles, so fluctuations are averaged out. Fur'hermore, the trarnport models include data from other tests that did not experience such fluctuations. The fluctuations are not believed to have affected vessel cooling in a way that could compromise the use of the LST for pressure, temperature, or transport predictions.
The extemal water flow rate is a relatively steady flow, interrupted by a periodic drop and recovery. Since the water coverage increases with time, the flow fluctuations prevent the coverage from reaching the maximum possible steady flow value. The separate effects data were evaluated using both the maximum ag minigum # flowgteg, sp ahve 3,3, approach was used for the data evaluation3AYtho'ug$Ithe flow vana'tions are considered a 8 distortion in the separate effects data, the use of maximum and muumum flow rates for data correlation adequately compensates. The film stability model uses a bounding approach that bounds both the 1:uximum and muumum data for film stability.
Crane Rails Are Not the Same - The LST lacked an intemal structure to simulate the stiffener nng located part way up the vessel side wall. The crane rail and stiffener ring strip the liquid film flowing down the inside surface. The film redevelops below these structures.
The stripped film is thmner and has a higher conductance than a film that is not stripped, bpt both conductances are so high they have little effect on AP600 performance Since the
- scaling analysis showed the film conductance was less than second order, relative to the l
other conductances, incomplete simulation in'the test has an insignificant effect on the results so is not a distortion at either the system level or component level.
l Distomons and Uses for the LST Revision 2 o:\3703w.d wptib-062397 June 1997 l
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Additional Markups to WCAP 14845 Rev 2," Scaling Analysis for AP600 Containment ;
l Pressure During Design Basis Accidents" l l
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7 15 The term that is of interest for scaling is the pool evaporation rate term. That term is normalized by the break steam flow rate and made dimensionless with the variable bevap.p
- Eevap,p,cb*evap,p:
m ,y ,p,p,o m ,y ,p,p,om ,y,p,p
[
j ,,
m MOP evap.p s&brk,o m g,brk,o %
(108) where xm,p =
s"8PP,0 g
The effect of the pool on containment pressure is manmized by assummg the liquid enters at the containment saturation temperature, similar to drops. Dunng the peak pressure and long-term time phases, saturated break liquid is assumed to flow across the top of the pool and to cool as it spreads. The net evaporation rate is the integrated evaporation flux over the surface area. The pool surface temperature was assumed to be at a steady-state with the spreading layer evaporating to the atmosphere, but not mixing or conducting to the cooler 1syer below. This maximizes the evaporation rate, resulting in the maximum pressure effect.
The resulting evaporation rates are presented in Table 7-2 for the peak pressure and long-crm time phases.
Durmg blowdown the high velocity jet and spray are assumed to produce sufficient liquid surface area to result in egmlibrium between the break liquid and atmosphere.
Consequently,' Equation (104) is used to calculate the evaporation (or flashing) flow rate. The results are presented in the first row of Table 7-2.
g Since the break flow rate drops to essentially zero during the refill time phase, the break pool cvaporation rate during refill is assumed to be zero.
The break pool surface area changes with time as the pool level rises. Since the analysis shows the evaporation rate is a small fraction of the flow into the pool, the pool liquid volume can be estimated as the integral of the flow rate over time. Using the liquid flow rates and times of each phase from Table 6-3, the pool volume at the start of each time phase was calculated and the pool surface area was deternuned from the relationship between break pool volume and surface area shown in Figure 3-8. The results are summarized in Table 7-3.
HIat Sink Analysis and Equations for Scaling Revtsion 2 e\37a3w.b wpub.062397 June 1997
10-24 Inspection of the detailed energy pi groups in Table 8-4 shows that dunng all the phases of a DECLG LOCA, phenomena associated with the drops, pools, chimney, and baffle are not important and can therefore be neglected since the pi group numerical values are of order less than 0.1. The only pi groups of any significance are those associated with the solid intemal heat sinks and the shell. However, the internal heat sinks become saturated prior to the time when quasi-steady operation occurs. Therefore, only the pi groups identified as containment or shell were calculated for the AP600 plant and the LST, at steady-state.
The results of the energy scaling comparison between the LST and AP600 are summarized in Table 10-3. The transient pi group n,,, is not applicable since d(mu)*/dt* = 0, that is, the containment atmosphere is in a quasi steady-state condition. Since the pi groups are normalized on break energy, n e.brk = 1.0. The table shows the dominant phenomena are condensation on the inside of the shell, n e.fg.ns, and evaporation on the exterior of the shell, n e.fg.e5x. The values for ne .fg.n, ande n .fs e5x in Table 10-Jhow the dominant phenomena p (condensation and evaporation) compare favorably. The shell energy phenomena for the subcooled and dry shell, n ,q,n3 o and n,,q,33x are shown to be second-order phenomena.
Although the pi values for subcooled and dry energy do not compare quite as well as those for condensation and evaporation, the former are second-order phenomena in both the plant and test, so distortions are not significant.
The scaling comparison permits the conclusion that the scaled LST represents the dominant intemal and external phenomena in AP600 with sufficient accuracy that the tests can be used to validate computer codes during quasi-steady (long-term) operation.
10.2.3 Scaling of the Transition Between the Initial Transient Phase and Quasi-Steady Phase There is no single LST experiment that is well scaled over the entire range of the AP600 DECLG LOCA. However, there is a wide range of LST experimental data that can cover the transient in a piece-wise fashion. The previous sections (10.2.1 and 10.2.2), for example, used different test runs to demonstrate that the LST adequately scales the initial transient range and long-term portions of the DECLG LOCA transient from a global, system level, for code validation purposes.
Test data at intermediate thermodynamic conditions (from the other test runs) could be used, applying the same scaling equations developed in Section 10.2.1 to conhrm scaling in the transition between the initial transient phase and the quasi-steady phase. However, this is not necessary since the system level scaling has already been shown to be adequate in both the initial and long term phases which bound the overall range of the transient.
Thus,it can be concluded that the use of the matrix of LST tests is sufficient for determuung the effect of MGOTHIC lumped parameter biases h application to AP600.
Evaluation of Scaled Tests Revision 2 o:\3703w.d wpHt>052597 June 1997
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ATTACHMENT 3 I Y Markups to WCAP-14812 Rev 1, " Accident Specification and Phenomena Evaluation for AP600 j
Passive Containment Cooling System" l
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The following comments consider Westinghouse response to discussion items that were raised L conceming WCAP 14811, Rev. O, the earlier version of the PIRT report, and how these are addressed in I WCAP 14812, Rev.1.
l 1. Time phases in Table 41 are not consistent with the scaling report, WCAP 14845, Rev. 2 (Table 6-3).
RESPONSE
The time phase difference results from the selection of different times for the peak pressure in the l PIRT and in the scaling analysis. The time for the PIRT peak pressure was defined from the l SSAR LOCA transient. The time for the scaling analysis peak pressure was selected for a j fictitious transient that produced a peak pressure equal to the design pressure. The latter case l
produced an upper limit for the scaling analysis.
l (2.) There still seems to be inconsistencies in the ranking of phenomena between the PIRT and scaling reports. For example, break source item 1E droplet /Fquid flashing is rated low for all accident phases but still appears in the list of medium and high ranked phenomena in Table 21 of the scaling report.
RESPONSE
_- The PIRT is the source document for ranking. The scaling analysis WCAP 14845, Table 21 will be revised to delete items from the column labeled " phenomenon" that are ranked Low for all phases of LOCA and MSLB. The items to be deleted are: 1E) droplet / liquid flashing,3A) Liquid Film Energy Transport, SF) Break Pool Compartment Filling (flooding level),7A) Convection from Containment, and 78) Radiation from Containment.
- 3. In Appendix A, Westinghouse has now at least identified the experts by name, but still hasn't I identified opinions and positions with an expert, so that the reader cannot tell who held what opinion. Also, source documents, such as written materials from the experts, are not included.
The value of the expert judgments is reduced considerably by the lack of information in this area.
RESPONSE
Westinghouse has considered the comments of the NRC, the ACRS, and the experts on source identification and believes the PIRT embodies the best balance. Source documents related to the expert review are available for NRC review at Westinghouse.
l 1.
v WCAP.14812, Rev.1 MARKUPS I
. . ~ _ _ _ . _ _ . _ _ . _ _ . _ . . _ . ~ _ . . . _ . _ . . . _ _ _ _ _ . . _m ___
" Pg. 2 3: The folloEing sentence is unclear:
L(4.)
v Such active systems in current PWRs lead to somewhat different thermal hydraulic conditions in AP600, so that AP600 specific verification was needed.
Suggest rephrasing the sentence with something like:
The absence of such active systems lead to somewhat...
RESPONSE
The text in WCAP-140 ? will be revised to clanfy the sentence.
- 5. Pg. 2-3/2-4: Scaling has been used to confirm the PlRT ranking (Ref. 2, Section ll) and' to specify the applicable data from the PCS Large Scale Test (Ref. 2, Section lil) for separate effects correlation validation and WGOTHIC code validation.
The same test data may have been used for both:
. a) deriving bounding correlations and b) for WGOTHIC code validation.
Multiple uses of the same data source may lead to circular arguments. Please discuss the procedures Westinghouse used to maintained the integrity of the validation studies. ,
' RESPONSE:
The same test can be used for both without introducing circular logic. For example, correlations for the mass transfer rate and for water coverage were determined from the LST data and validated without use of the code. The models were built into, or input to the code, and it was
.- verified that the code gave the same mass transfer rate and coverage predictions. This is not circular. The code was then used to predict pressure in the LST and compared to measurements.
Since the individual models and the pressure calculations use independent data, the logic is not circular.
L
- 6. ' Pg. 2 4: Westinghouse states that the integral LST facility included a representation of the AP600 intemals. Although the LST intemals did not represent inter compartment flow paths, data from l LST have been considered in addressing stratification since the LST test matrix addressed a l- range of imposed boundary conditions. Does this limit the LST data applicabili*y to stratification only? -
L RESPONSE:
l
- No, it limits the LST to use as separate effects test data and as integral effects that do not include similarity of intemal circulation.
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(7.) Pg. 2 9: Section 2.2.7 LST, States:
, Long term heat and mass transfer test data for a geometrically similar model of the AP600 containment vessel..., . determining the relative importance of various parameter that affect heat and mass transfer on both inside/outside containment surfaces.
What does relative importance means? What is the measure?
RESPONSE
The sentence will be revised something like " . . for determining the sensitivity of the heat and mass transfer rates inside and outside containment to various parameters."
(8.) Pg. 211: In the LST, a diffuser was located under a simulated steam gerierator companment below operating deck (LOCA simulated). Steam rose in a plume, and air was entrained in the rising plume resulting in a natural circulation flow pattem within the simulated containment.
However, a diffuser under a simulated SG compartment in LST does not provide anything close to real break simulation (LOCA blowdown). How can a plume develop for an unconfined SG? LST l lacks a second SG compartment, therefore flows and entrainment are atypical of AP600.
RESPONSE: l The paragraph that precedes the subject paragraph states "The LST did not simulate the j blowdown phase of the LOCA or MSLB transients." The text in the subject paragraph will be revised to state that the diffuser simulated the break igg.ation a of a LOCA. l l
1 Pg. 211 : Section 2.3 : Scaling Analysis (9.) Last paragraph, Westinghouse states :
In Reference 2, Sect. Ill, top-down scaling is used to determine the most important system level phenomena during blowdown and long term phases of a large break LOCA transient and to show how well those phenomena are preserved between LST and the AP600 plant. The results of this analysis are used to determine to what extent global containment data (pressure) can be used from LST for WGOTHIC code validation. This contradicts the statements in Section 2.2.7 stating the LST did not simulate the blowdown chase, j
RESPONSE
Section 2.2.7 of WCAP 14812, Rev.1 (3rd paragraph) will be revised. The sentence, "The LST did not simulate the blowdown phase of the LOCA and MSLB transients.' will be deleted. The last
- sentence of the paragraph will be revised to read, 'LST tests were performed over a range of l initial and boundary conditions to assess the impact on heat and mass transfer rates, and to provide a sufficient history of thermodynamic conditions to adequately simulate the quasi-steady long term cooling phase of an AP600 transient."
The last paragraph of WCAP 14845, Rev. 2 Section 10.2.1.3 provides further clarification of the use of LST data during the blowdown phase of the transient.
l WCAP 14812. Rev.1 MARKUPS 3
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l Pg. 3 5 : Sect. 3.2.1 Inside Containment
_, 10. The break source definition (For what break? LOCA7 MSLB7) is not detailed enough as it only relates to the blowdown phase. The water drops suspended in the steam indial!y flash a small fraction of their mass to steam to reach thermal equilibrium within the containment atmosphere.
l
RESPONSE
1 Sections 3.2.1,3.22, and 3.2.3 are brief, general descriptions of the two major regions (inside and )
outside) that are separaied by the shell. It is not intended to be detailed, but rather, to encompass 1 both LOCA and MSLB transients. The details of the Evaluation Model are presented in WCAP- l 14407, Rev.1, Section 4.
- 11. After flashing, the large surface area of these many tiny water drops maintains the atmosphere at or near saturation for up to thousands of seconds. Westinghouse needs to provide references i and experimental evidence. l
RESPONSE
The scenario in questio1 was postulated as an extreme (drops may very well not persist for more i than a few 10's of seconds) that is analyzed to determine how significant an effect drops can I have, both drop thermal and momentum effects. The outcome of the analysis is that both effects are ranked low for all time phases. Therefore, the effects of real drops are no more important than these hypothetical drops.
- 12. All compartments below-deck are provided with top openings to minimize the potential for a dead pocket of noncondensible concentration. However, this is not applicable for higher up break positions for steel jacketed concrete (explanation missing). The break liquid which is not dispersed as drops is assumed to leave the break at the containment saturation pressure 1
RESPONSE
Break liquid not dispersed as drops is addressed in Section 4.4.1E (PIRT).
The geometry of the internal heat sinks above the operating deck is also designed to minimize the potential for dead pockets of noncondensibles.
WCAP.14812, Rev.1 MARKUPS
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i Additional agenda items:
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. Ref.: Loftus, M.; Spencer, D.; Woodcock, J., " Accident Specification and Phenomena Evaluation for AP600 Passive Containment Cooling System," WCAP 14812, Rev.1, June 1997 The following general observations, issues and comments are provided conceming WCAP 14812, Rev.1:
- 1) The current PIRT report is not code-independent but rather merges PIRTs, WGOTHIC Evaluation Model aspects and uncertainty issues in one and the same document. This should be reflected in the title of the report.
COMMENT:
THE COMMENT l$ NOTED AND ACKNOWLEDGEO THAT BOTH _WGOTHIC, ASPECTS OF THE EVALUATION MODEL AND CERTAIN ELEMENTS OF UNCERTAINTY ISSUES ARE DISCUSSED IN THE CURRENT PIRT REPORT. 'THE PRIMARY FOCUS OF THE CURRENT PIRT DOCUMENT IS TO PRESENT AND DISCUSS THE PIRT. IT IS NOTED THAT WGOTHIC, THE EVALUATION MODEL AND UNCERTAINTY ISSUES ARE DISCUSSEO TO THE EXTENT THEY SUPPORT DEVELOPMENT AND UNDERSTANDING OF THE PIRT. THUS, THE TITLE OF THE DOCUMENT IS INDICATIVE OF ITS CONTENT AND NO CH)NGE IN THE TITLE OF THE CURRENT PIRT REPORTIS PLANNEO.
(2.) The ranking rationale as displayed on pg. 4-20 deviates from PIRT guidelines as it lists both energy transfer process and containment pressure. The chosen wording opens many avenues
- , for ambiguity and speculation. If it is decided to really keep two objective functions, namely
' energy transfer process" and ' containment pressure reduction" then the items in the ranking rationale should correctly read " increase in energy transfer' and resultant " containment pressure -
- reduction." This could be also reconciled by eliminating the word " reduction."
COMMENT:
CONTAINMENT PRESSURE WAS THE PREFERRED FIGURE OF MERIT USEO FOR THE PIRT.
HOWEVER, CONTAINMENT PRESSURE IS MEANINGFUL ONLY FOR PARAMETERS DEFINED INSIDE l THE CONTAINMENT SHELL. FOR PARAMETERS CONSIDEREO EXTERNAL TO THE CONTAINMENT l SHELL, THE ENERGY TRANSFER PROCESS WAS USED AS THE FIGURE OF MERIT. THE TEXT WILL BE AMENDED TO CLARIFY THIS.
WCAP 14812, Rev.1 MARnUPS 5
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- 3) Although the ranking rationale encompasses both energy transfer process and containment j pressure, the texts, references and arguments for the individual phenomenon in the main body of the repolt refers to the containment pressure only for the majority of them because this is the only figure of merit for which results have o' een provided.
COMMENT:
CONTAINMENT PRESSURE WAS THE PREFERREO FIGURE OF MERIT USED FOR THE PIRT.
HOWEVER, CONTAINMENT PRESSURE IS MEANINGFUL FOR PARAMETERS DEFINED INSIDE THE CONTAlNMENT SHELL. FOR PARAMETERS CONSIDERED EXTERNAL TO THE CONTAINMENT SHELL, THE ENERGY TRANSFER PROCESS WAS USED AS THE FIGURE OF MERIT.
- 4) Westinghouse has applied the bounding methodology for High-ranked phenomena, such as for - )
instance for the most important energy transfer processes: condensation and evaporation inside and outside the containment, respectively, rather than as recommended for the Low-ranked phenomena.
COMMENT:
THE APPROACH TAKEN BY WESTINGHOUSE TREATS LOW RANKED PHENOMENA IN A CONSERVATIVE MANNER. NO CHANGE TO THIS CONSERVATIVE TREATMENT OF LOW-RANKED PHENOMENA IS PLANNEO.
- 5) The basis for PIRT ranking is not based on experimental evidence (even for High-ranked phenomena) as would be expected. Rather, the majority of PIRT ranking is based on scaling calculations, done using a special code with a simple model of the containment.
COMMENT:
l S DESCRIBED IN THE DOCUMENT, THE BASIS FOR THE PIRT IS HISTORICAL EXPERIMENTAL DATA WHERE AVAILABLE, HISTORICAL CALCULATIONS, ANO EXPERT OPINION. THE DATA, ANALYSES AND EXPERT ODINION USED TO DEVELOP THE PIRT ARE DESCRIBED UNDER THE TITLE, ' BASIS FOR PIRT RANKING,' GIVEN FOR EACH PHENOMENA LISTED IN THE PIRT. BRIEF DESCRIPTIONS OF TESTS USED FOR DEVELOPMENT OF THE PIRT ARE GIVEN IN SECTION 4.3 OF - \
THE DOCUMENT. EXPERT OPINION USED IN DEVELOPMENT OF THE PIRT IS GIVEN IN APPENDIX A OF THE DOCUMENT. OPTIMAL USE OF AVAILABLE EXPERIMENTAL DATA WAS MADE IN DEVELOPING THE PIRT.
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..s a = s.a.es. -a x,.n- - u. . - - - .n < n. e -.sa+a-- s -sm.~ ~ - .ss- -
I (6.) Although the majority of PlRT-rankings is based on the results of scaling considerations and j l . expert review, Westinghouse did not specify criteria for the numerical values for the PI-ratios for which the importance of a phenomenon would be ranked differenti/ although they have essentially the same values for the PI ratios. This leads to a non uniform ranking, rationale and resultant I confusion.
l COMMENT:
SEE ATTACHED RESPONSC,
- 7) Westinghouse has evaluated the PI-ratios at the beginning of a time phase. Some physical quantities drastically change over the time phase but this change was not evaluated. Therefore, the numerical FI ratio evaluated at the beginning of the next time phase, for instance, refill, results in a very much different (higher) value. In some cases, Westinghouse noticed and commented on these discrepancies. However for the majority of phenomenon the low predicted PI-ratios were taken at face value and the phenomenon ranked ' Low' for this time phase without any furiher considerations. This uneven approach leads to a number of ambiguities and concems.
l COMMENT:
l IF A PI-GROUP WAS RATED EITHER 'HIGH' OF ' MEDIUM
- FOR THE ENTIRE TRANSIENT WITH RESPECT TO TREATMENTIN THE EVALUATION MODEL.
i 8) Most subsections in the discussions on phenomena are geared too much toward the LOCA time phase, although MSLB results in the highest computed containment pressure by the AP600 EM. i In most descriptions, MSLB is not mentioned at all except for the PIRT-ranking. This may be acceptable for equally ranked phenomena, but for all other cases this may pose the potential for l omitting important information. The non-uniform treatment of LOCA and MSLB time phases does not seem justified.
COMMENT:
THE CONTAINMENT RESPONSE TO A LOCA IS MORE COMPLEX THAN THAT FOR A 00STULATED MSLB. THE APPARENT FOCUS OF ATTENTION ON A LOCA IS THE RESUL1 OF ACCOUNTING FOR l
THE INCREASED COMPLEXITY OF THE CONTAINMENT RESPONSE TO A LOCA. WHEN MSLB HAS A UNIQUE ASPECT, IT IS DISCUSSED.
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- 9) Some high-ranked phenomena, such as evaporation of the externalliquid film, require the success of a medium- and low-ranked phenomenon, i.e., PCS riser annulus natural circulation, vapor acceleration, fog and flow stabihty. Based on this PIRT, modelers may mistakenly downgrade the conservatism of models associated with entical systems.
COMMENT:
RANKING A PHENOMENA As ' LOW" INDICATES THAT THE PHENOMENA HAS A SMALL EFFECT ON PRESSURE. IT COULD BE TREATED WITH REALISTIC OR BEST ESTIMA TE MODELS, OR IGNOPED IF SUCH TREATS'NT WOULD BE CONSERVATIVE. SIMlU.RL Y, PHENOMENA RANKED AS A
' MEDIUM
- AT ANY TIME DURING THE TRANSIENT WERE SPECIFICALLY CONSIDERED DURING IN THE EVALUA TION MODEL AND WOULD BE IGNORED ONLY IF TO DO SO WO:)LD BE CONSERVA TIVE (RESULTIN A PRESSUREINCREASE). THuS, THE CONSERVATISM ASSOCIATED WITH TREATMENT OF PHENOMENA RANKED AS "HIGH" WAS NOT CHALLENGED BY EITHER " MEDIUM" OR " LOW" RANKED PHENOMENA.
- 10) Westinghouse may not be crediting the expert review efforts, because of the following reasons:
a) The export review is no substitute for an independent PIRT panel.
b) There is not a single phenomenon for which Westinghouse has adopted the experts' different ranking. Rather the experts' opinions were dismissed and the results of the scaling PI ratios were adopted (compare comment under point) maintaining
,,. Westinghouse's original ranking. Most often the experts ranked the phenomenon higher but Westinghouse consistently downgraded the rank.
This is acceptable only for phenomena for which an in-depth knowledge and experimental database exists. Most often this is not the case in the ranking should tend toward higher than r
lower importance.
COMMENT:
WHEFF THE PIRT RANKING DEVELOPED BY NESTiNGHOUSE D!FFERED FROM THAT OF EXPERT y REVIEW, .IUSTIFICATION FOR THE DIFFEREhCE WAS GIVEN. THE REVIEW OF DIFFERING OPINIONS AND DEVELOPMENT OF RATIONALE ACCEPTING OR RE.IECTING EXPERT REVIEW IS ALSO PART OF THE PIRT PROCESS. !!'IS WESTINGHOUSE'S OPINION THAT THE JUSTIFICATION DEVELOPED FOR VARYING FROM THE EXPERT REVIEW RANKING AND PRESENTED IN REVISION 1 OF WCAP-14812 IS TECHNICALL Y VALID.
c r
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WCAP.14812. Rev.1 MARKUPS 8
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, 11) Descriptions under the headline "How Phenomenon is Implemented in Evaluation Model" do not
'j actually refer to the implementation but rather to input quantities or general descriptions of the phenomenon / process in or between components / subsystems, in fact, for many phenomena the text is a repeat of at least parts of the genera! introductory description of the phenomenon under consideration. Under the headline one would expect reference to models, correlations / procedures implemented in WGOTHIC.
COMMENT:
THE DESCRIPTIONS ARE GENERALLY
SUMMARY
STATEMENTS. HOWEVER, WHERE THE DETAILS MAY BE FOUND ARE INCLUDED BY REFERENCE. INCLUSION OF ALL DETAILS *N THIS REPORT WOULD HAVE BEEN REPETITIOUS AND MADE THE REPORT UNWIELDY AND OlFFICULT TO USE. l DETAILS OF THE IMPLEMENTATIONIN WGOTHIC IS FOUND IN WCAP 14407.
l
- 12) Westinghouse lists a number of " Test Experience" under the headline " Justification for EM l
Treatment of Phenomenon." However, for many phenomena this consists only of a test j description or reference of a correlation which is not really a justification. Under justification it l would be expected to reference results how the containment pressure / energy transfer processes l are affected using the cited correlation in comparison with data. This has not been done l consistently, rather sensitivity studies and LST-result comparisons are references. In hindsight, l
the test experience cited should well have been referenced as basis for the PIRT-ranking (compare comment under point) rather than for justification of WGOTHIC AP600 EM. l l
. COMMENT:
THE INFORMATION SUGGESTED IN THIS COMMENT IS INCLUDED BY hEFERENCE. INCLUSION OF THE DETAILS IN THIS REPORT WOULO HAVE BEEN REPETITIOUS AND RESULTED IN AN UNWlELOY REPORT.
WCAP 14812. Rev.1 MARKUPS 9
I lasues Related to the Ranking of Specific Phenomena and Treatment in EM l 1
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General comment: The phenomena listed under the components are not systematically handled in terms of time phases in Section 4.1.
Pg. 4-8 Table 41
- 1) Westinghouse ranks all characteristics (direction, elevation, momentum, density) of (1) Break Source " Low" during LOCA long-term. Equally, inter-compartment flow for (2) Containment volume is ranked " Low" for LOCA blowdown phase and so on. Given the fact that LST did not consistently cover all these phenomena with respect to AP600 requ:rements, the ranking seems too low especially when considering the impact of " memory effect" of early heatup in one region of the plant on global natural circulation pattem during the LOCA long term time phase. This concern also encompasses the inter-compartment flows as this determines the region of initial heatup.
COMMENT: .
I 1
THE BASIS FOR THE RANKING OF BREAK SOURCE PHENOMENA AS BEING " LOW" OURING THE LONG TERM LOCA IS 3ASED ON KNOWING THAT MASS AND ENERGY RELEASES ARE SMALL DURING THIS TIME PERIOD, NOTON TEST DATA. SIMILARLY, FOR INTER-COMPARTMENTAL FLOW, THE " LOW" RANKING IS BASED ON SENSITIVITY STUDIES WHICH SHOW THE DETAILS OF THE FLOW PATHS ARENOTIMPORTANT.
- 2) The component / subsystem (5) Break pool does not list pool heatup as a phenomena. Is there any special consideration why Westinghouse has disregard this potential source for energy release during long term?
COMMENT:
DURING THE LONG TERM, THE BREAK POOL FLOODS UP TO ABOVE THE BREAK LOCATION. HEAT-UP OF THE BREAK POOL IS BY CONDENSATION OF STEAM ON THE SURFACE OF THE BREAK POOL.
SINCE, l.ONG TERM, THE BREAK POOL IS RELATIVEL Y OUIESCENT (LOW FLOW OUT THE BREAK),
THE CONDENSATION PROCESS IS LIMITED BY THE FORMATION OF A W/RM LAYER OF FLUID ON THE TOP OF THE BREAK POOL. THUS, THE HEA TUP OF THE BREAK POOL IS LIMITED.
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- 3) Under point (7) Steel Shell and energy transport phenomena have been ranked either " Low" or j ' Medium", yet the energy removal from the film evaporation (ranked High) is mandatory in order to
~
guarantee the efficiency of the passive PCS cooling. Westinghouse is asked to provide information about the ranking rationale applied for energy transport phenomena in the downcomer riser component.
COMMENT:
THE PRIMARY COOLING MECHANISM FOR THE AP600 CONTAINMENTIS BY EVAPORATION OF THE PCS FLOW. THUS, AS LONG AS WATER IS APPLIED TO THE EXTERNAL SURFACE OF THE PCS SHELL, IT IS EXPECTED THAT THERMAL ENERGY TRANSPORT MECHANISMS OTHER THAN EVAPORATION WOULD BE RANKED AS EITHER MEDIUM OR LOW. OF COURSE, IF THE SHELL WERE WSULATED, THEN THERE WOULD BE NO ENERGY TRANSFER. HOWEVER, THE PURPOSE OF THE RANKING IS TO MAKE JUDGEMENTS REGARDING THE IMPACT OF UNCERTAINTIES ASSOCIATED WITH INDIVIDUAL ENERGY TRANSPORT PROCESSES. THUS, IN RANKING THE CONDUCTION THROUGH THE STEEL SHELL, NOTING THAT IT REPRESENTS ONLY ABOUT 1/3 OF THE TOTAL RESISTANCE AND THAT SHELL THICKNESS IS WELL CONTROLLED, THE EXPERTS AGREED THAT CONDUCTION THROUGH THE SHELL SHOULD BE RANKED OF LOWER IMPORTANCE THAN CONDENSATION OR EVAPORATION.
- 4) Under point (8) PCS Cooling Water, subpoint D) Film Striping received only " Low' ranks for all time phases, yet this is the cause for introducing a correction for accounting for 2 D heat
~
conduction effects to increaso film evaporation. Westinghouse is asked to explain the " Low" ranking for this phenomena even for later phases when film flow is low.
l COMMENT:
THIS SECTION IS " STRIPPING," WHICH REFERS TO THE DETACHMENT OF THE LIOUID FILM FROM THE EXTERNAL SURFACE OF THE 3 HELL DUE TO SHEAR FORCES FROM THE PCS AIR FLOW, AND NOT ' STRIPING," WHICH PEFERS TO THE FORMATION OF ALTERNATING WET AND DRY STRIPES OF WATER AS IT FLOWS DOWN THE OUTSIC.~ OF THE CONTAINMENT SHELL. THE ' STRIPPING" PHENOMENA IS APPROPRIATELY RANKED AS BEING ' LOW.'
i 4
i i
J 4 WCAP 14812 Rev,1 MARKUPS If
.. _ _. _ ~. _ . . _ . _ _ _._
- 5) Under point (10) Baffle, subpoint G) potential leaks through the baffle are ranked " Medium" for j LOCA time phases peak pressure and long-term. Westinghouse is asked to explain this ranking
~
in view of the fact that this poses a potential threat for short-circuiting and thereby disabling the natural draft effuct.
COMMENT:
THE RANKING ACKNOWLEDGES THE POTENTIAL IMPORTANCE OF BAFFLE LEAKAGE. THE INTRODUCTORY TEXT ALSO NOTES THAT EXPERIMENTAL DATA FOR RECTANGULAR CROSS.
SECTION CHANNELS SHOWS BAFFLES HAVING LIMITED EFFECT ON HEAT TRANSFER. WHILE NOT EVALUATED AS BEING A DOMINATE PHENOMENA, THE RANKING OF " MEDIUM" ASSURES THE PHENOMENA IS ADDRESSED IN THE AP600 CONTAINMENT EVALUATION MODEL.
SHORT-CIRCUITING MAS BEEN EVALUATED WITH SENSITIVITIES AND SHOWN TO BE A MEDIUM EFFECT. NOTE ALSO THAT THE EVALUATION MODEL INCLUDES A FLOW PATH ACROSS THE BAFFLE TO ACCOUNT FOR THE POTENTIAL FOR LEAKAGE.
- 6) Under point 13) Downcomer, subpoints A) PCS Natural Circulation and B) Air Flow Stability are ranked " Medium" and " Low", respectively, yet the efficiency of the PCS system depend very much' on sustaining both phenomena, for transport purposes of the evaporation mass and energy from the cooling film. Westinghouse is asked to provide the ranking rationale for both phenomena given their importance for the fun:tionality of the PCS cooling concept.
COMMENT:
FOR PCS NATURAL CIRCULATION, THE RANKING OF MEDIUM WAS BASED ON STUDIES SHOWING THE SENSITIVITY OF THE PCS AIR FLOW TO HYDRAULIC PARAMETERS WAS SMALL.
FOR AIR FLOW STABILITY, THE RANKING OF LOW WAS BASED ON SCALING THE ENERGY AND MOMENTUM ASSOCIATED WITH THE FLOW PATH. THE STUDY SHOWED THAT ENERGY ADDITION TO .THE DOWNCOMER FROM THE BAFFLE WAS SMALL AND THE MOMENTUM OF A BUOYANT BOUNDARY LAYER WOULD NOT DISRUPT THE ESTABLISHED NATURAL CIRCULATION FLOW. THUS THE POTENTIAL FOR INSTABILITY TO OCCUR IN THE PCS AIR FLOW PATH IS NEGLIGIBLE, AND THE y PHENOMENON IS THEREFORE RANKED LOW.
WCAP 14812. Rev.1 MARKUPS 12
s Pg. 416 1
~i Westinghouse states that increased heat transfer coefficients were observed when the steam jet directly impinges on the horizontal plate and that this simulates the steamline break. Westinghouse is asked to provide information why this is the case, given the fact that the realistic break positions for both LOCA and i MSLB are still not displayed in the associated figures.
COMMENT:
THE SUBJECT FIGURE 3-2 CLEARLY SHOWS THE PRIMARY SYSTEM PIPE WHICH GOES FROM THE STEAM GENERATOR TO THE REACTOR VESSEL AT THE BOTTOM OF THE STEAM GENERATOR COMPARTMENT, AND THE MAIN STEAM LINE WHICH LEAVES THE TOP OF THE STEAM GENERATOR AND PASSES THROUGH THE CMT COMPARTMENT BEFORE IT PENETRATES THE CONTAINMENT SHELL. IF THE READER IS INTERESTED IN MORE DETAIL, HE IS REFERRED TO WCAP-14407, c FIGURE 9-36, WHICH SHOWS IN MORE DETAIL THE ARRANGEMENT AND VARIOUS DIRECTIONS AND MOMENTUM EFFECTS EVALUATED IN ESTABLISHING THE L!MITING LOCA AND MSLB SCENARIOS. THE STATEMENT REFERS TO OBSERVED BEHAVIOR IN EXPERIMENTS. THE TEST WAS DESIGNED TO SIMULATE CONDITIONS EXPECTED FROM A STEAM LINE BREAK THAT WOULD RESULTIN STEAM IMPINGING DIRECTLY ON THE CONTAINMENT WALL. THE SUBJECT TEXT IS NOT i INTENDED TO IMPLY THA T ALL STEAMLINE BREAKS WOULO RESULTIN A STEAM JETIMPINGING ON THE CONTAINMENT SHELL. .
Pg. 417 i Westinghouse reports observations from the Small Scale PCS Integral Tests concerning higher than vessel averaged heat removal at the top of the dome. However, the phenomenon of non-uniformity in heat transfer is not listed in the PIRTs. Does this mean that this phenomenon has not been observed during LST-tests?
COMMENT:
IN REVIEWING THE PIRT FORMAT WITH EXPERTS, IT WAS AGREED THAT AN APPROPRIATE LEVEL OF DETAIL WAS INCLUDED IN THE PIRT. THE ADDITION OF ALL PARAMETERS WHICH INFLUENCE EACH PHENOMENON WOULO MAKE THE PIRT UNWIELDY AND REDUCE ITS USEFULNESS.
PARAMETERS WHICH INFLUENCE IMPORTANT PHENOMENA ARE EVALUATED IN ESTABLISHING THE RELEVANT ELEMcNTS OF THE CONSERVATIVE EVALUATION MODEL. NON-UNIFORMITY OF HEAT FLUX IS ENCOMPASSED BY OTHER PHENOMENA LISTED IN THE PIRT. THE SUPPLEMENTAL INFORMATION REFERENCEO IN THE PIRT POINTS THE READER TO THE SUPPLEMENTAL ;
DOCUMENTA TION WHERE MORF DETAll MA Y BE FOUNO. i NON-UNIFORMITY OF HEAT FLUX IS ADDRESSRO IN THE CIRCULATION AND STRATIFICATION SUPPORTING ELEMENTS OF THE EVALUATION MODEL BASED ON INTERNATIONAL TEST DATA THAT INCLUDES VARIOUS EXTERNAL BOUNDARY CONDITIONS WITH AND WITHOUT EXTERNAL WATER
, (SECTION 9.C.2 OF WCAP-14407). THE INFLUENCE OF AXIALLY VARYING HEAT FLUX ON ;
.- EXTERNAL WATER COVERAGE IS INCLUDED IN THE SECTION 7 WATER COVERAGE EVALUATION.
WCAP 14812. Rev.1 MARKUPS 13 l
a Pg. 417 v
- 1) .' Westinghouse reports film behavior during the LST PCS Integral Testo, yet is unclear what the goveming heat fluxes were at the outside steel shell surface and how they compare with the relevant ones for AP600.
COMMENT:
f ADDITIONAL DISCUSSION IS PROVIDED IN SECTION 7 OF WCAP-14407. ALSO, TABLE 7-5 COMPARES HEAT FLUXES FROM PCS LARGE SCALE TESTS AND TABLE 7-10 LISTS ESTIMATED HEAT FLUXES FOR THE AP600 UNDER VARIOUS CONDITIONS.
- 2) in this context, Westinghouse states that " striped film coverage provided better heat removal than forced quadrant ceverage for the same wetted perimeter." is this statament referring to an experimental setup or to a calculational exercise? -
COMMENT:
. THIS IS BASED ON COMPARISON OF OBSERVATIONS FROM LARGE SCALE TESTS 207.1, 207.2 AND 207.3 AND 207.4 AS DESCRIBED IN SECTION 2.1.2 AND SUMMARIZED IN TABLE 2-3 OF REPORT PCS-T2R-050, 'LARGE-SCALE TEST DATA EVALUATION."
I 1
- 3) Westinghouse states that heat removal rate appeared to be more affected by ambient air i s temperature than by liquid film temperature. Yet, ambient air temperature was ranked " Low."
Westinghouse is asked to explain this effect and whether this effect has been observed in all tests.
COMMENT:
THE CONCLUSION REGARDING RELATIVE EFFECTS OF AMBIENT TEMPERATURE AND FILM
. TEMPERATURS IS DIRECTLY DERIVED FROM LST DATA AS STATED IN THE REFERENCE 38 LST TEST ANALYSIS REPORT. THE RANKING IS AN INDICATION THAT BOTH EFFECTS WERE SMALL, AND THAT AMBIENT AIR TEMPERATURE WAS THE LARGER OF TWO SMALL EFFECTS. AMBIENT AIR TEMPERATURE DETERMINES THE BUOYANCY HEAD THAT CAN BE GENERATED. THIS BEHAVIOR MA Y BE NOTED IN ANY TEST WHERE THE VARIABLE IS THE AMBIENT TEMPERA TURE.
)
1 WCAP 14812. Rev.1 MARKUPS 14
. . -- . _ . . . . . . . .- . . . - . . .. .-- - - ~ _ . .
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. 4) Westinghouse reports that also during the LST-test non-uniform heat flux was observed. Why has this phenomenon not be included in the PIRTs? This deems especially important for the horizontal, high-velocity steam jet injection. Please explain.
COMMENT:
IN REVIEWING THE PIRT FORMAT WITH EXPERTS, IT WAS AGREED THAT AN APPROPRIATE LEVEL OF DETAll WAS INCLUDED IN THE PIRT. THE ADDITION OF ALL PARAMETERS WHICH INFLUENCE EACH PHENOMENON WOULD MAKE THE PIRT UNWIELDY AND REDUCE ITS USEFULNESS.
PARAMETERS WHICH INFLUENCE IMPORTANT PHENOMENA ARE EVALUATED IN ESTABLISHING THE RELEVANT ELEMENTS OF THE CONSERVATIVE EVALUATION MODEL. NON-UNIFORMITY OF HEAT FLUX IS ENCOMPASSED BY OTHER PHENOMENA LISTED IN THE PIRT. THE SUPPLEMENTAL l lhFORMATION REFERENCED IN THE PIRT POINTS THE 9EADER TO THE SUPPLEMENTAL DOCUMENTA TION WHERE MORE DETAIL MA Y BE FOUND. l NON-UNIFORMITY OF HEAT FLUX IS ADDRESSED IN THE CIRCULATION AND STRATIFICATION SUPPORTING ELEMENTS OF THE EVALUATION MODEL BASED ON rNTERNATIONAL TEST DATA THAT l INCLUDES VARIOUS EXTERNAL BOUNDARY CONDITIONS WITH AND WITHOUT EXTERNAL WATER (SECTION 9.C.2 OF WCAP 14407). THE INFLUENCE OF AXIALLY VARYING HEAT FLUX ON !
EXTERNAL WATER COVERAGE IS INCLUDED IN THE SECTION 7 WATER COVERAGE EVALUATION.
- 5) Westinghouse states that by raising the steam injection location, heat removal rate increased as the steam concentration near the containment shell increases. This is true but this oositive effect
-, is offset by the reduction in steam concentration at lower levels by stratification. Westinghouse is asked to provide more quantitative results for these observatic is.
COMMENT:
A DETAILED DISCUSSION ON THE OBSERVATIONS ASSOCIATED WITH THIS BEHAVIOR IS INCLUDED IN SECTION 2.4, ' STEAM INJECTION LOCATION AND FLOW RATE
- OF PCS-T2R-050, 'LARGE-SCALE TEST DATA EVALUATION
- l WCAP 14812. Rev.1 MARKUPS 15
e
^'
- General F:emarks -
' The summary presentation of experimental results has largely improved and is more focused than before.
However, most information are of qualitative, descriptive nature, rather than quantitative solid evidence.
Overall, the list of findings seems still too sholt. The findings should be structured such that the results are directly related to the phenomenon under consideration.
COMMENT; THE DISCUSSION PROVIDED IN THIS REPORT IS A
SUMMARY
. OETA!LS OF EXPERIMENTAL RESULTS USED TO SUPPORT DEVELOPMENT OF THE PIRT ARE INCLUDED BY SPECIFIC REFERENCES TO APPLICABLE REPORTS IN THE DISCUS $10NS.
Pg. 419 Outside Containment Westinghouse states that "the buoyancy cod flow resistance in the PCS air flow path are important and have a strong effect on the evaporation rate." However, both buoyancy and flow resistance are not listed as phenomenorvparameter in the P! FIT. If it is assumed that both phenomena were considered to be ;
cc' ered by." natural circulation", these phenomena would only be ranked medium, an apparent Jinconsistency.
,; : COMMENT; A MEDIUM RANKING FOR NATURAL CIRCULATION IS APPROPRIATE. IT IS IMPORTANT BUT IS 1 SECONO ORDER RELATIVE TO EVAPORATION WHICH IS RANKED HIGH. SENSITIVITIES TO THESE PARAMETERS IS PROVIDED IN WCAP-14407.
i
-k W""_
n-WCAP 14812. Rev.1 MARKUPS 16
23 l
Table 21 Phenomena identification and Rankmg Table - Summary of High and Medium Ranked
_.'} Phenomena Phenomenon
- EL%<t on Containment Pi Groups Where Addressed Break Source Mass and The only mass and energy source ap4brk.d Scaling Analysis
+g Enerev (1A) for contamment pressunzation n psbrk. work
~ 7#(E;.% ; ._' and Kp. work.a Evaporacon (58) K,. work.,
Gas Compliance (2C) Stores mass and energy in up,, Scahne, ^ntlysis atmosphere, increasing pressure ..
4 Initial Conditions Inside Temperature, humidity, pressure Non2 Initial Conditions (4A, 49, 4Q affect noncondensables and energy Ref. 5, Section 5 storage Containment Solid Heat Sinks (3), Pool (5), Drops Store energy (and remove mass from atmosphere) reducing F[
xp 3
Scahng Analysis 7 (1), and Shell (7) pressure
- Internal Heat Sink Limits conduction heat transfer parameter Scahng Analysis Conduction (3I% into heat sinks, shell, or pool, and SE; 75 end Heat through shell. Stratification in the l Cap (W, q break pool can affect the effective heat capacity of the pool.
) ,
Heat Transfer Water and noncondensible layers parameter Scahng Analysis
, Through Horizontal on upward facing horizontal 2
s Liquid Films @ surfaces limit heat and mass transfer to horizontal heat sinks
- Condensation Mass The single first-order transport xp,,,,g,; Scahng Analysis Transfer (3P,M S process that removes mass and
, energy from the contamment gas F'reak Source Dtrection, elevation, density, and parameter Circulation and
[Arection and momentum can dominate Stratification, Ref. 5, Section 9 Elevation W crculation and affect condensation Momentum ( rate. Existence of droplets in Density source during blowdown affects h- Wn i. 7 the effective source density.
Circulation and Intercompartment Flow Stratification W (Circulation) and stratification can affect the distribution of steam parameters IntC near heat sinks for conden',ation Flow heat removal. "M; '@ h ;d Qq S ': i- s c ' t = S -
Y# L ,68]N e
Source Fog @ Affects arculation and parameter stranfication vu buoyancy Dommant Phenomena Revision 2 cxs3mw+wpMb.062497 June 1997
Table 21 Phenomena Identification and Rankmg Table Summary of Hi6h and Medium Ranked
- (cont.) Phenomena i .
l Phenomenon
- Effect on Containr:wt Pi Groups Where Addressed Evaporation Mass h first-ord.ar trangort process x,4,, Scahng Analysis Transfer W that removes mass and energy from the evaporating extemal shell 1
PCS Natural Convective air flow provides parameter Scaling Analysis l Circulation M convective heat and mus transfer M from contamment shell.
- Liquid Film Flow Affects the upper limit for water parameer Film Stability,
- Rate hWat coverage on the external shell Ref. 5, Section 7 Temperature Film Stability N i Liquid F Inside
h Transport Carries 14 percent of condensation energy to the IRWST and break x,g Scahng Analysis pool. See note 1 Outside:
Absorbs 8 percent of energy Te,p ssy, rejected by the extemal sheu surface.
C cat Transfer xp4 g M A second order transport process that removes energy from the Scahng Analysis x,+x,4 14A) contamment gas, and from the da Note 2 extemal sheH.
L. Ra cat Transfer A second order transport process sp4 Scahng Analysis
- T that removes energy from the x,4,,+ x,4 contamment gas and from the da extemal sheu. Note 2 Baffle Conduction Conduction through the baffle into x,43 PIRT Sections and Baffle I.makage pa downcomer volume and leakage x,pg 4A.10D and m) paths can irfluence the extemal None for 4.4.10G natural circulation flow rates leakage Indacators in parentheses refer to phenomena in the " Phenomena Identification and Rankmg According to Effect on Contamment Pressure" (R4--w 3, Table 4-1).
Note 1. The fraction of the intamal condensation energy carned away by Ne liquid film is defined by the goes ratio: x4 (bcooled h'est capacity of the extemal bquid is,4,,
into the su defined by the ratio: x
/(x,g+
x,,+x,4, +x,4 da) The Pi group values for AP600 are presented in Section 8 p
Note 2. Inside heat transfer contamment is approximately u h2 radiation heat transfer and 1/2 convection heat transfer.
re contamment that is approxunate x,4,,ly 1/2 radiation heat trarafer and 1/2 convection heat transfer.+x,w pr
=#
Dommant Phenomena Revtszon 2 eJMwAwytite June 1997
2-3 2.2 TESTING PROGRAMS The need for tests to support the AP600 containment design was identified in the late 1980s.
At that time, containment phenomena with chsracteristics that were unique to AP600 were identified and an initial testing program was defined. The following provides an overview of the test program structured to address 10CFR52.47(b)(2)(i)(A), subsections (1) and (3).
The design basis events calculated for the SSAR are used as a starting point to examine the types of data needed to support containment DBA. Each transient type is examined to see how the tatiqueness of the AP600 design imposes additional model verification requirements on the safety analysis code, WGOTHIC, and supporting models. The differences between the existing PWRs and the AP600 are also considered, since the basis for many of the safety analysis criteria and methods is rooted in the bases for the current generation of PWRs.
The phenomena were compared to the available contairunent test database (Table 2-1) to indicate the need for additional tests for validating analytical models. The important thermal hydraulic phenomena were identified, and the existing verification for the safety analysis codes was assessed against the current verification of the code, as well as the applicability of the data verification for the AP600 design. The assessment indicated which models required additional verification for the AP600 specific geometry or conditions. The assessment also gave an initial indication of which phenomena are of mcst impcrtance for representing the
, passive features of the AP600 safety systems. Although many of the phenomena occur in current PWRs, there are no safety grade active containment cooling systems credited for the containment DBA in the AP60035uch active systems in$~% """b lead [to somewhat $
different thermal hydraulic co 'tiorkin , so that AP600 specific verification was needed. Test programs were stablished ddress:
we sem op cuue d N Rs evaporation and condensation mass transfer, including the effects of hydrogen, external air cooling of the steel shell, a internal circulation and stratification, ;
external liquid film distnbution (stacility and coverage), !
. effects of wind and turbulence,
. integral tests focused on long term heat and mass transfer data (the LST).
Separate effects tests were performed at vanous facilities, as discussed below. Becau;e the initial blowdown period for AP600 is not significantly different from that of current operating plants, integral effects tests, focused on the long term cooling for AP600, were identified to examme the integrated heat and mass transfer behavior of the PCS.
Subsequent to the design of the PCS integral test facilities, scaling methods developed in the 1940s have been applied as described in NUREG/CR-5809. Scaling has been used to confirm the PIRT ranking (Reference 2,Section II) and to specify the applicable data from the PCS ,
l l
PROCES3 FOR PHENOMENA IDENTIFICATION AND RANKLNG Revision 1 3692w.wpf.lb-060697 4
. . =- -- .- . - ._
2-9 2.2.6 Small-Scale PCS Integral Tests I s I 1
The small-scale tests were designed to provide heat and mass transfer data for both the !
inside and outside of the test vessel. The test apparatus consisted of a 3-ft. diameter,24-ft.
high, steel pressure vessel that was i:iternally heated by steam. The vessel was surrounded by a clear, plexiglass shield that formed a 15-in. wide annulus for either forced or natural l circulation air flow. The tests were performed with varying steam flow rates, water film flow I rates and temperatures, and inlet air flow rates, temperatures, and humidity. I Instrumentation was provided to measure internal steam concentrations, external water l evaporation rates, exit film temperatures, air velocity and temperature, and humidity. See Reference 14 for more information on small-scale tests.
2.2.7 Large-Scale PCS Integral Tests l l
The large-scale PCS test (LST) facility was built to provide long term heat and mass transfer test data for a geometrically similar model of the AP600 contai:unent vessel. The tests provided experimental data for evaluating phenomena inside contamment, and for determining thegd:-. hp 'r : d .r.dc.; pruc.d=: S.:t ;did heat and mass transferf"'
4-
= 5 0. ,insige and outside contamment,ewdaees. +o various paraW5.
<ent.kvay of N. l The LST consisted of a 15-ft. diameter,20-ft. high pressure vessel that approximated the AP600 contamment vessel at approximately 1/8th linear scale. A plexiglass cylinder was installed around the vessel to form the air cooling annulus (also called the riser in this report). Air flows upward through the annulus via natural circulation to cool the vessel. A fan was located at the top of the annular shell to provide the capability to induce higher air ,
velocities than can be achieved during natural circulation alone, so that riser Reynolds l numbers in the range of AP600 could be simulated. A liquid film was applied to the outside of the test vessel to provide evaporative cooling. Two rings of I-tubes provided the capability to apply water in a manner sinular to the water coverage observed in the water distribution tests. See Figure 2-2 for m overview of this test facility.
Test conditions were selected to provide steady-state heat and mass transfer data over a range of conditions representative of a DBA. These conditions included pressure, steam flowrate, cooling air brate, and water coverage. The IST was designed to sufficiently encompass the conditions expected during long term cooling for the most limiting AP600 transients such as a large cold leg LOCA and MSLB. h Lyd c.e: 3 blewdcr . A J L LOC /. mm MSLO _.cr. bhes testsswere performed over a range of *)w initial and boundarv conditions to assess the impact on heat and mass transfer rates, and provide, a suffic.ied hMhey of ectmodynamic, condikans 4o adephe\y sim\ak 4ke, i- 5Veady bm3h erm (6ohy phase of an A%00 t raed.
PROCESS FOR PHENOMENA IDENIIFICATION AND RANKING Revuion 1 3692w.wp61t460697
, % becaM \och.
. For most tests, steam was injected through a diffuser located under a simulated steam generator compartment below the operating deck (which simulated,a LOCA} The steam M-rose as a plume, and air was entrained in the rising pliune resulting in a natural circulation j flow pattern within the simulated contamment. Thermocouples located on the inner and outer surfaces of the vessel were used to determine the temperature and heat flux g g g4 distributions. Tests were also performed with an elevated steam source to simulate an .por MSLB, with parametric variations to examine the effect of source direction and momentum.
See Refcrences 15 and 16 for more information on these tests.
2.3 SCALING ANALYSES The scaling analysis results have been used to support quantification of the importance of I various phenomena in the contamment cooling process (Reference 17). The scaling analysts ;
performed for the AP600 containment was submitted for review and revised to incorporate l NRC comments (References 2,18). 1 In Reference 2,Section II, control volume equations were developed to describe the rate of !
change of the containment gas energy and pressure. These equations were coupled by l conductances to energy equations for internal heat sinks and to the external PCS through the j shell. l Scaling groups (PI groups) were developed by normahzing and nondimensionabzing the conservation equations, using initial and boundary conditions, in a form that shows the l important dimensionless parameters in each group. Values were calculated for the PI groups I during each time phase to quantify the relative importance of the transport processes and components. The evaluation of the PI groups assumed that the containment steam / air j atmosphere was well mixed. Nondimensional parameters and relevant test data were defined for assessing stratification and internal flow field stability.
The PI grcups were evaluated for containment energy and pressunzation, conductances to heat sinks and the shell, momentum in the air flow path, and momentum within the containment. The conclusions from the scaling analysis, which suppor' the importance of the phenomena identified in the PIRT, are discussed in subsection 4.3.2.
In Reference 2,Section III, top-down scaling is used to determme the most important system level phenomena dunng blowdown and long term phases of a Large LOCA transient and to show how well that phenomena are preserved between the LST and AP600 plant. The results of this analysis are used to determine to what extent global contamment data (i.e.
contammet a ssure) can be used from the Large Scale Test r. _,1) for WGothic code validation
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l'ROCESS FOR PHENOMENA IDENTIFICATION AND RANKING Revtston 1 3692w.wpf1beue97
~
b Additiemal agenda Isease:
i
- 3. Ref.: ' Loftus,'M.; Spencer, D.t Woodcock,1, " Accident Specification and Phenomena Evaluation for AP600 Passive Containment Cooling System," WCAP 14812, Rev.1. June 1997
' ' . .<J '
~ The following general observations, issues and comments are provided concerning WCAP 14812, Rev.1:
2). The ranking rationale as displayed on pg. 4 20 deviates from PIRT guidelines as it lists both energy transfer process and containment pressure. The chosen wording opens many avenues for ambiguity and speculation.
If it is decided to really keep two objective functions, namely " energy transfer process
- and " containment pressure reduction" then the items in the ranking rationale should correctly read " increase in energy transfer" and resultant " containment pressure reduction." This could be also reconciled by eliminating the word " reduction."
Comment:
lo clarify this point, thu text of the first paragraph under " Basis for Ranking" will be rep!sced with the following; The phenomena relevant to the containment response to a DBA are shown in the PIRT (Table 4-1). The PIRT has been structured into high, medium and low rankings consistent with the discussion in subsection 4.2. Phenomena were
- ranked based on their effect on containment pressure as deduced from test te suits, scaling analysis results, sensitivity studies, expert review and engineering judgement.
I Containment pressure was the preferred figure of merit used for the PIRT for containment pressure scaling.
However, containment pressure is meaningful only for those parameters defined inside the containment shell i (The pressure of the ambient atmosphere is unaffected by the energy transfer from the containment shell.)
L For parameters considered external to the containnant stell, the energy transfer process was used as the figure of merit.
l:
l l
I I
s.
d se 4.***
4 .-- 6
- 6) Although the majority of PIRT-rankings is based on the results of scaling considerations and expert review, ,
Westinghouse did not specify critena for the numerical values for the PI-ratios for which the importance I of a phenomenon would be ranked differently although they have essentialiy the same values for the f PI ration. This leads to a non-uniform ranking, rationale and resultant confusion.
1 CoMMurr: 1 The numerical critena for establishing a ranking for a phenomenon, based on the scaling analysis results, l was, i Low - 0.0 to 0.10 Medium - 0.11 to 0.20 High . > 0.21 I l
There were a small number of phenomena for which scaling results and expert opinion did not agree. The rationale for select ing the ranking for the phenomenon listed in the PIRT, as well as the phenomena to
. Nich that rationale was applied, are summanzed below:
Scenario 1: Scaling results rank phenomenon as
- Low," expert opinion ranks phenomenon higher; phenomenon listed as
- Low
- in PIRT. j Basir Sensitivity studies performed to study the effect of the phenomenon supported a PIRT ;
ranking of " Low." Numerical results were given greater weight than expert opinion in setting the PIRT ranking to " Low."
The phenomena to which this scenano was applied in letermining its PIRT ranking are listed in the table below.
PIRT Table Component Phenomenon Title i or Volume 1(c) Droplet / Liquid Flashing 3(a) Liquid Film Energy Transport on Containment Heat Sinks l 5(a) Break Pool Circulation / Stratification 5(b) Br:sk Pool Condensation / Evaporation f
7(a) Convection Heat Transfer from Contamment Volume 7(b) Radiation Heat Transfer from Containment Volume to Steel Shell l 7(e) Internal Film Energy Transport on Steel Shell L
13(a) PCS Natural Circulation" 4
Notes: (1) The ranking of
- Low" for this phenomenor. does not indicate that the presence of natural i cinulation is unimportant to the predicted AP600 containment response. Rather, sensitivity studies indicate there is a small vanation in predicted containment pressures over the range of hydraulic resistances considered for natural circulation air flow for the AP600 design. This is pnmanly due to the self-compensating nature of the buoyancy.
... 7
6 driven flow; higher hydraulic resistance results in lower air flow which results in higher air temperatures which increases the buoyant forces which increases air velocity which increases the air flow rate.
s Scenario 2: Expert opinion ranks the phenomenon as ' Low," scaling results ranks the phenomenon higher; phenomenon listed as " Medium" or "High" in PIRT.
Basis: In the absence of corroborating numerical resula (sensitivity calculations), the higher ranking of the experts was assigned to the phenomenon in the PIRT.
The phenomena to which this scenario was applied in determining their PIRT ranking are listed in the table below.
PIRT Table Component Phenomenon Title or Volume 3(g) Convection from Containment Volume 3(h) Radiation from Containment Volume to Contatament Heat Sinks l
Scenario 3: This scenario was applicable to these phenomena transferring energy from the containment atmosphere to and through the containment shell; condensation on the inside surface of the shell, heat capacitance of th: shell, and thermal conductivity through the shell. In compartng the ranking obtained from expert opinion and scaling calctilations, the highest ranking was selected for the PIRT. If the ranking obtained from expert opinion and scaling calculations agreed, that ranking was entered into the PIRT.
Basis: The success of the PCS is dependent upon transferring energy from the containment atmosphere through the containment shell to the ambient environment. Conservatively ranking the importance of those phenomena assures they will be appropriately addressed in the AP600 containment Evaluation Model. 4 1
1 The phenomene to which this scenario was applied in determining its PIRT ranking are listed in the table l l below.
i PIRT Table l Component Phenomenon Title i or Volume l
i 7(c) Condensation on Inside Containment Shell I
7(f) Conduction Through Shell 7(g) Heat Capacity of Shell It is also noted that all phenomena ranked as " medium
- or "high" in at least one phase of the transient were treated in the same manner for the entire transient. That is, those phenomena were explicitly included in the AP600 containment evaluation model.
.- 8
- l. .
., Westingtiouse Energy Systems sai355 Rectfic Corp 0 fail 00 Pmsburgn Pennsylvania 15230 0355 s_./
DCP/NRCl413 NSD-NRC-98-5757 Docket No.: 52 003 August 14,1998 Document Control Desk i U. S. Nuclear Regulatory Commission Washington, DC 20555
)
ATTENTION; T. R. Quay
SUBJECT:
RESPONSE TO NRC LETTERS CONCERNING REQUEST FOR WITHHOLDING INFORMATION
Reference:
- 1. Letter, Sebrosky to McIntyre, " Request for withholding information from public disclosure for Westinghouse AP600 design !ctter of October 20,1933," dated June 18,1998.
- 2. Letter, Sebrosky to McIntyre, " Request for withholding information from public disclosure for Westinghouse AP600 design letter of January 17,1994," dated June 18,1998.
s
- 3. Letter, Sebrosky to McIntyre, " Request for withholding information from public disclosure for Westinghouse AP600 letters of September 20,1993, January 21, 1994, and ISbruary 3,1994," dated July 10,1998.
- 4. Letter, Sebrosky to McIntyre, " Request for withholding proprietary infarmation for Westinghouse letters dated April 18,1995," dated July 15,1998.
- 5. Letter, Huffman to McIntyre, " Request for withholding information from public disclosure of Westinghouse report on AP600 function based task analysis," dated July 17,1998.
Dear Mr. Quay:
Reference 1 provided the NRC assessment of the Westinghouse claim that proprietary information was prosided in a letter dated October 20,1993, that contained the response to a staff request for additional information regarding the AP600 probabilistic risk assessment. The NRC assessment was that the material was similar to material that exists in the current (1998) nonproprietary version of the AP600 probabilistic risk assessinent (PRA) report. In addition, the staff indicated the material was used by the staff in the development of the AP600 draft safety evaluation report and therefore should remain on the docket. At the time this request for additional information respcnse was provided to the _
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NRC technical staff, the information was considered to be proprietary by Westinghouse since it contained information that had commercial value to Westinghouse. If this request for additional information response was indeed used by the staffin development of the AP600 draft final safety evaluation report in November 30,1994, then at this time, almost five years later, this information is no longer considered to be proprietary by Westinghouse.
Reference 2 provided the NRC assessment of the Westinghouse claim that proprietary information was provided in a setter dated January 17,1994, that contained the response to a staff request for additional information regarding the AP600 instrumentation and control system. The NRC assessment was that the material " ts similar to material that exists in the current (1998) norproprietary version of the AP600 sundard safety analysis report. In addition, the staff indicated the material was used by the l staff in the development of the AP600 draft safety evaluation report and therefore should r main on the docket. At the time this request for additional information response was provided to the NRC technical staff, the information was considered to be proprietary by Westinghouse since it contained information that had commercial value to Westinghouse. If this request for additional information response was indeed used by the staffin development of the AP600 draft final safety evaluation report in November 30,1994, then at this time, over four years later, this information is no longer considered !
to be propric*ary by Westinghouse.
Reference 3 provided the NRC assessment of the Westinghouse claim that proprietary information was provided in a letter dated September 20,1993, that contained information related to the AP600 PRA and WCAP-13795, which provided the PRA uncertainty analysis.' The NRC assessment was that the material ws.s similar to material that exists in the current (1998) nonproprietary sersion of the AP600 probabilistic risk assessment (PRA) report. In addition, the staff indicated the material was used by the staffin the development of the AP600 draft safety evaluation report and therefore should remain on the docket. At the time this information was provided to the NRC technical staff, it was considered to be proprietry by Westinghouse since it contained information that had commercial value to Westinghouse. If the information transmitted by the Westinghouse September 20,1993, letter was indeed used by the staffin developmen: of the AP600 draft final safety evaluation report in November 30,1994, then at this time, almost five years later, this information is no longer considered to be poprietary by Westinghouse.
Reference 3 also provided the NRC assessment of the Westinghouse claim that proprietary information was provided in a letter dated January 21,1994, that contained WCAP 13913. " Framework for AP600 Severe Accident Management Guidance" (SAMG). The NRC assessment was that the material was similar to material that exists in current (1998) nonproprietary AP600 documents (e.g., WCAP 13914,
" Framework for AP600 Severe Accident Management Guidance"). In addition, the staffindicated the material was used by the staff in the development of the AP600 draft safety evaluation report and therefore should remain on the docket. At the time this Framework for SAMG was provided to the NRC technical staff, the information was considered to be proprietary by Westinghouse since it contained information that had commercial value to Westinghouse. At this time, over four years later.
- this information is no longer considered to be proprietary by Westinghouse.
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DC'P/NRCl413 NSD NRC-98 5757 3- August 14,1998 Reference 3 also provided the NRC assessment of the Westinghouse claim that proprietary information was provided in a letter dated February 3,1994, that contained additional copies of WCAP-13913,
" Framework for AP600 Severe Accident Management Guidance"(SAMG). ne NRC assessment was that the material was similar to meaerial that exists in current (1998) nonproprictary AP600 documents (e.g , WCAP 13914, "Framcwork for AP600 Severe Accident Management Guidance"). In addition, the staff indicated the material was used by the staffin the development of the AP600 draft safety evaluation report and therefore should remain on the docket. At the time this Framework for SAMG was provided to the NRC technical staff, the information was considered to be proprietary by Westinghouse since it contained information that had commercial value to Westinghouse. At this time, over four years later, this information is no longer considered to be proprietary by Westinghouse.
Reference 4 provided the NRC assessment of the Westinghouse claim that proprietary information was provided in a letter dated April 18,1995, that contained information for a MAAP4/RELAP comparison for the AP600 in response to a staff request for additional information. The NRC assessment was that the Westinghouse cover letter indicated that Enclosure 2 is a non proprietary version of Enclosure 3, however, the staff could not tind any portion of the enclosures marked as proprietary. The staff assessment further states the conventional bracketed-superscript notation also appears to be missing.
Finally, the NRC assessment states the staff could not determine which part of the material enclosed with the Westinghouse letter was Enclosure 1,2, or 3. It should be noted that the Westinghouse April i 18,1995, cover letter states " Enclosures 2 (nonproprietary) and 3 (proprietary) provide the requested ,
information." The letter does not indicate that enclosure 2 was a duplicate of enclosure 3 minus the '
proprietary infonnation. A cover sheet was provided just prior to each of the enclosures to the Westinghouse letter. De enclosures contained the following: Enclosure I provided a copy of the NRC's two page request for info,mation for the MAAP RELAP comparison. Enclosure 2 provided the requested information, and was titled " Requested Information for AP600 MAAP4/RELAP Comparison." Under section 4, Initial Conditions, of Enclosure 2 it states the initial conditions information (which was proprietary) is provided in Enclosure 3 of the subject Westinghouse letter.
Finally, Enclosure 3 cor.tained the list of initial :onditions. He information provided in Enclosure 3 was labeled as Westinghouse Proprietary Class 2 at the top of the page, however, the specific proprietary information was not indicated by the bracketed-superscripted notation. In addition to the Initial conditions, a mark up of APf300 PRA Figure K 1 was provided in Enclosure 3. Again, the information was labeled as Westinghouse Proprietary Class 2 at the top of the page, however, the specific proprietary information was not indicated by the bracketed superscripted notation. At the time the information provided in Enclosure 3 of the subject Westinghouse letter was provided to the NRC technical staff, the information was considered to be proprietary by Westinghouse since it contained information that had commercial value to Westinghouse. At this time, over three years later, this information is no longer considered to be proprietary by Westinghouse.
l Reference 5 provided the NRC assessment of the Westinghouse cla:m that proprietary information was provided in a letter dated February 8,1994, provided a copy of WCAP-13957,"AP600 Reactor l Coolant System Mass Inventory: Function Based Risk Analysis." He NRC assessment was that the material was not "information that the staff customarily accepts as proprietary." In addition, the stati indicated the material was used by the staff in the development of the AP600 final safety evaluation report and therefor: should remain on the docket. At the time this report was prepared, the mt 40/CO*d 2002G1r10Cl9 01 244r PLC 2tr 371!ri3OdHOW-3dd dd 80:G1 86.r1 9rW
i 4
DCP/NRCl4I3 NSD-NRC-98 5757 4- August 14,1998 information was considered to be proprietary by Westinghouse since it contained infonnation that had commercial value to Westinghouse and was of the type ofinformation that was customarily held in confidence by Westinghouse. That the material was not information that the staff customarily accepts as proprietary is not :: levant to making the proprietary determination. However, in an effort to expedite the issuance of the AP600 Final Safety Evaluation Report and Final Design Approval, Westinghouse agrees to no longer consider this infonnation to be proprietary, in a telephone call on July 8,1998, the staffinfonned Westinghouse of a concern related to WCAP-13288 and WCAP-13289, which were associated with the AP600 check valve testing specification The concern was that the proprietary report had no proprietary information identified and the ncioproprietary report had been placed in the public document room. Westinghouse has reviewed these reports and, at this time, considers none of the information to be proprietary.
This response addresses the proprietary issues delineated in the references.
A #
Brian A. McIntyre, Mana Advanced Plant Safety and Licensing jml cc: J. W. Roe NRC/NRR/DRPM J. M. Sebrosky - NRC/NRR/DRPM W. C. Huffman - NRC/NRR/DRPM H. A. Sepp - Westinghouse l nm.,r 40/PO*d -2002GIPIOCIB 01 2LLP PLC 2fr 3771n30dNOW-Odd d .i. 60*GI 86.P! One