ML18142B974
| ML18142B974 | |
| Person / Time | |
|---|---|
| Site: | Ginna  |
| Issue date: | 02/15/1978 |
| From: | Amish K Rochester Gas & Electric Corp |
| To: | Schwencer A Office of Nuclear Reactor Regulation |
| References | |
| Download: ML18142B974 (59) | |
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0 I/IEISÃZJIII I/IIIIT'III ii:l7/lsll.';;,'-me.pre'Tg">>(9, 'HlNI%-:E.: -
I ROCHESTER GAS AND ELECTRIC CORPORA ON o
89 EAST AVENUE, ROCHESTER, N.Y. 14649 KSITH W. AMISH EXECUTIVE VICE PRESIDENT TELEPHONE
- REACODETIE 546-2700 February 15, 1978
'./>@PE '4) 4t ~ilgwu~+
Director of Nuclear Reactor Regulation ATTN:
Mr. A. Schwencer, Chief Operating Reactors Branch 41 U.
S. Nuclear Regulatory Commission Washington, DC 20555
Dear Mr. Schwencer:
Your letter of February 10, 1978 requested additional in-
'formation concerning the adequacy of our ECCS evaluation model.
The ~equested information is included in Attachment A.
Most of this information was gathered together for presenta-tion to members o'f the NRC staff on February 9,.1978, and there-f'ore includes information for all of the Westinghouse two-loop plants as well as information specific to R.'E. Ginna.
Sincer ly yours,
~'/a Keith W. Amish r-7SOe7ooeg
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ATTACHMENT A
RESPONSE
TO FEBRUARY 10, 1978 REQUEST FOR ADDITIONAL INFORMATION I
Question 1.
Provide the Westinghouse design FZECHT correlation used in the analysis including all input parameters.
RESPONSE
Figure 1 is taken from the FZECHT studies~
~.
This figure was used to draw Figure 24 in the SER.
The FZECHT reflood conditions for the line used by the staff are shown in Table 1.
Also on Table 1 are shown the comparative two loop plant reflood condi-tions. It can clearly be seen that Figure 24'f the SER is not representative of the two loop plants.
To amend this situation, the Westinghouse approved i
FZECHT correlation was used with the input '.from, Table 1 which is more appropriate for two loop plants.
Figure 2 shows the results.
The most important difference between Figure 2 and Figure 24 in the SER is the reduction of peak power from 1.24 Kw/Ft to 0.75 Kw/Ft.
This reduces the slope of the curve.
- Thus, a smaller increase in clad temperature will occur for a given reduction in flooding rate if the fuel rods are at a lower power.
t t
Question 2.
Provide the input values for pressure, injection rates, flooding rates and decay heat as a function of time used in the analysis and provide references for the sources of this data.
RESPONSE
Figures 3 through 14 show the flooding rate, decay heat and core pressure transients used.
The cases shown are the worst break case from the latest Westinghouse
-analysis submitted to the NRC for each plant.
These analyses were sent by letter for each plant as follows:
Plant Ginna Point Beach 162 Praire Island 162 Keuwanee Date of Letter 4/07/77 10/27/76 1/20/77 12/10/76 Note that transient injection flowrate capability was available but, not used.
For the above plants, con-stant injection rates of 440 lb/sec, 440 lb/sec, 480 lb/sec and 480 lb/sec, respectively, were used.
l'
Question 3.
Provide the carryover rate fraction as a function of time for a typical two-loop plant reflood.
RESPONSE
The carryover fraction, CRF, discussed on page 40 of the SER was changed from 0.8 in the "staff model" to 0.7.
Figure 15 shows a typical carryover fraction transient.
- Clearly, a value of 0.7 is more repre-sentative of the transient.
This change results in higher peak clad temperatures.
Question 4.
Provide the heat transfer coefficient and the steam generation in the unquenched portion of the core due to bottom reflood water.
RESPONSE
The SER sighted FLECHT SET Phase A tests 5703 and 6007 Table 2 compares the test conditions for
[3]
these tests to a Westinghouse designed two loop plant.
Table 2 indicates that use of tests 5703 and 6007 is conservative in terms of steam genera-tion rate.
The lack of a large quantity of data may justify the conservative use of this data; however, it is felt that the way this data was used in the "staff model" was not appropriate.
Figure 16 is from WCAP-8238 and was Figure 6 in the SER.
The staff stated that, in test 5703, the top injected water was able to cool the rod at a rate of 1'F/sec.
For test 6007 a cooldown rate of 2'F/sec was assumed.
WCAP-8238 clearly states that the improved core heat. transfer in test 6007 as compared to test 5703 (2 F/sec versus 1'F/sec) was due to the water allowed to accumulate in the bottom of the bundle in test 6007.
- Thus, simultaneous top and bottom flooding occurred in test 6007 and some of the heat transfer was going to bottom generated steam.
Also, the semiscale tests referenced in the SER~
indicate that some of the heat transfer in the un-quenched region is to the bottom generated steam.
Pi'gure 17 is a plot of heater rod temperature rise versus time for the midplane of semiscale tests S-05-6 and S-05-7.
The former test had no upper plenum injection.
The latter test had upper plenum injection.
U.P.I. did not greatly improve core heat transfer before quench time.
The upper regions of the core did quench faster with UPI, however.
The point to be made here though is the amount, of heat transfer to the bottom generated steam flow.
Since tests S-05-6 and S-05-7 both resulted in similar rod temperature transients, the heat transfer to steam in the unquenched region was relatively unchanged.
In test S-05-6, all of this heat transfer was to the bottom generated steam.
In test S-05-7, the amount of heat,,transfer to be bottom steam probably ranges from the same as in test S-05-6 near the bottom quench front to a fraction of test S-05-6,.near the top quench front.
Based on the ratio of top generated steam flow to bottom. generated steam flow about half of the heat transfer in the unquenched region would be going to the bottom steam and half'o the top steam.
C
The test data does not allow a good determination of the fraction of heat transfer in the unquenched region which is going to the bottom steam.
- However, the available data does indicate modification to the "staff model".
The clad temperature turnaround time for the 1520 Mwt two-loop plants is 50 seconds after "flood".
From Figure 16 it can clearly be seen that the clad is heating up rather than.cooling down for this period of time.
The 1650 Mwt plants turn-around in less than 250 seconds after flood.
Figure 16 again indicates that the clad is hotter at 250 seconds that it was at the initiation of flood.
At best, the top injection is barely keeping up with the simulated decay heat at 250 seconds after flood.
The SER also references the "G-2, 17x17 Refill Heat Transfer Tests and Analysis" report, WCAP-8793-P Test 763 in this report is a
typical test.
A temperature transient for this test is shown on Figure 18.
The average heat-up rate during the 60 seconds of upper head injection is +O'F/sec.
Figure 19, however, shows that the G-2 test power was about 40% greater than a typical two-loop
plant.
In the staff model it is assumed that a 2'F/sec temperature ramp is equivalent. to about 30% of decay heat.
If the G-2 power had been re-duced by 40%, the heat up rate might be something like
+ 5'F/sec
.x 2'F/sec
= +2.33'F/sec.
40 30 In other words, in test 763 of the G-2 tests, top injection is not. even able to remove decay heat.
The G-2 heater rods are not cooling down by 2'F/sec but rather heating up.
The same statement can be made concerning the Semi-scale Test S-05-7 discussed earlier (Figure 17).
The "staff model" transferred 130% of the decay heat in the unquenched core region based on the above tests and the assumed 2'F/sec cooldown rate.
A review of the same data, especially the FLECHT-SET Phase A Tests, indicates that only about 80% of decay heat is being removed.
This essentially reduces the "staff model" heat transfer to the UPI water by 25%.
Question 5.
Provide a list of the sources of metal heat in the upper plenum along with the mass and stored energy of each.
Question 6.
Provide a description of the heat release model em-ployed in the upper plenum, including the assumed heat transfer coefficient, surface area and specific heat.
RESPONSE
Table 3 summarizes the mass of metal, m, located in the upper plenum of a typical two loop plant.
Use of the total metal in the upper pie'num is conserva-tive because half of it, including the upper support plate, is above the injection ports and will not communicate with the UPI water.
However, all of the metal shown in Table 3 was used in the Westinghouse analysis.
These same values are used in the SATAN-VI blowdown calculation.
To initialize the reflood calculation, the temperature of this metal at the end of blowdown, T., is found from SATAN-VI.
The amount of metal heat, is then found from the follow-ing eguation:
Q=m.
C (T -T) where C
is, of course, the specific heat of the metal p
and T is the saturation temperature at core pressure.
The Westinghouse model assumes the UPI water is heated up from 70'F to 150'F a change of 80'F until all of Q is removed from the metal.
This corresponds to a heat transfer coefficient of about 112 BTU/Ft hr
. 'F.
This coefficient was changed from 10 to 140 without changing the final answer in terms of average flooding rate.
This should be expected since the change in average flooding rate is proportional to the UPI steam generation and is not changed but only redistributed in the transient.
Question 7.
Provide a calculation of the change in peak clad temperature for each two-loop plant using the Westinghouse proposed model with proposed changes 4
and 5 eliminated for both 100% ANS decay heat, and 120% ANS decay heat.
Question 8.
Provide the appropriate changes in F and/or power q
levels, if necessary, for each two-loop plant to assure that the results of each of the above calcula-tions (item 7) meet the peak clad temperature criterion of 2200 F.
RESPONSE
Calculations were performed using the Westinghouse proposed model with proposed changes 4 and 5
eliminated although no basis for removing these changes is apparent and we continue to believe that proposed changes 4 and 5 are fully justified.
The results are summarized in Table 4.
These calcula-tions show a benefit for most cases compared to the current documented peak clad temperature.
The peak clad temperatures for all the plants including R. E. Ginna are below the 2200'F limit of 10 CFR 50.46.
Therefore, no changes in FQ and/or power level are proposed.
References:
1.
- Cadek, F. F., et. al.,
"PWR FLECHT Final Report Supplement",
WCAP-7931, October, 1972.
2.
- Bordelon, F. M., et. al.,
"LOCTA-IV Program:
Loss of Coolant Transient Analysis",
- June, 1974.
3.
Blaisdell,'J. A., et. al.,
"PWR FLECHT SET Phase A Report",
WCAP-8238, December 1973.
4.
- Feldman, E. M., et. al.,
"Experimental Data Report for Semiscale Mode 1 Tests S-05-6 and S-05-7 (Alternate ECC Injection Tests)"
TREE-NUREG-1055,
- June, 1977.
TABLE 1 Parameter Figure 3-26 WCAP-7931 2-Loop Plant, Explanation Value Used On Fi re 2 1.
Initial Peak Rod Power (Kw/Ft) 2.
Initial Rod Peak Temperature
('F) 3.
Injection Flow Subcooling ('F) 1.24 1600 16-28 0.75 1800 50*
Figure 3-26 is unrealistic and too conservative (Use 0.75 Kw/Ft)
No significant. effect because of initial temperature (Use 1600'F)
(Use 30'F) 4.
Pressure (PSIA) 60 35 Non-conservative to use 60 psia (Use 35 psia.)
- Estimate based on UPI water being saturated when it reaches the lower plenum consistent with staff steam generation model).
TABLE 2 Parameter
- l. Initial Peak Rod Local Power (Kw/Ft) 2.
Injection Flow Per Assembly (lb/sec) 3.
Initial Peak Rod Temperature
('F) 4.
Injection Flow Subcooling ('F) 5.
Pressure
.FLECHT Set, A Tests 5703
& 6007 0.7 4.0 1100 60 15 psia 2-Loo Plant 0.7 0.75 4.0 1800 100 180 35 psig Ez lanations About the same About the same No significant effect as shown by tests 5703 and 5904 FLECHT Set. Phase A is conserva-tive as shown 'by tests
- 5703, 6106 and 6408 FLECHT Set Phase A is conservative because of the same effect as injection flow subcooling
TABLE 3 Com onent Upper Coreplate Upper Support Plate Lower Guide Tube Assembly Deep Beam Weldment Upper Support Columns Flow Mixing Columns Hold Down Springs Thermocouple Assemblies 2,270 19,000 10,125 7,021 9,280 2,074 1,900 675 138 3,142 178 827 96 23 3
TABLE 4 UPPER PLENUM INJECTION RESULTS CURRENT WESTINGHOUSE EVALUATION MODEL ANALYSIS I
NEW U.P.I.
ANALYSIS PEAK CLAD TEMPERATURE PEAK CLAD TEMPERATURE 1.0 ANS 1.2 ANS Decay Heat; Decay Heat WEP/WIS RGE NSP/NRP WPS 2.32 2.32 2.32 2.25 1965 1957 2187 2172 2.32 2.32 2.32 2.25 1945 1900 2110 2090 2025 1972 2177 2162
1000 900 800 700 600 500
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1 200 100 90 80 n
60 5p
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~ 20 10 0,$
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'J SYHBOL' CLAD nF l6nn l600 l600 1600 PRESSURE PSIA 60 IS-20 18-2l 60 SUBCOOLIHG oF l42 l42 85-53 l6-28 PEAK POWER KW/FT l.24 I ~ 24 l.24 l.24 ti.p
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