ML20038C020
| ML20038C020 | |
| Person / Time | |
|---|---|
| Site: | Sequoyah  |
| Issue date: | 11/16/1981 |
| From: | TENNESSEE VALLEY AUTHORITY |
| To: | |
| Shared Package | |
| ML19268A511 | List: |
| References | |
| NUDOCS 8112090426 | |
| Download: ML20038C020 (300) | |
Text
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I h7AcNMEN7 b SEQUOYAH NUCLEAR PLANT CON ~iAINMENT RESPONSd TL. DEGRAP G CORE EiENTS Nove:nber 16, '.981 kN 8112090426 811201 PDR ADOCK 05000327 P PDR
r OUTLINE A. S2 D Base Cas. Analysis B. SD 2 Sensitivity Runs j C. Scenarios D. Core Recovery E. Conclusions References I
. .J l
l l
l L ..
A. S2D Base Case Analysis Introdnetton Hydrogen transient analyses, including the effects of passive heat sinks, have been performed for the Sequoyah containment using the new version of the CLASIX computer program (Reference 1). As in the case of previous Sequoyah analyses (Reference 2) hydrogen generation was assumed to occur during a degraded core event resulting from a small break loss of coolant accident with failure of safety injection (S2 D).
Recovery of core cooling was still assumed to occur prior to core slump.
Major changes have been made in this base case run that were not included in previous submittals, including our Iane 2, 1981, submittal on equipment su rv iv ab il i ty. In particular, the air return fans model was modified to discharge to the dead-ended compartments instead of the lower compartment to accurately depict the plant configuration. The location of all igniter: were reviewed r.nd burn times were changed to reflect the distance between igniters and the number of igniters in each compartment and to assume simultaneous ignition at all ignitees in a compartment The unmber and location of igniters have changed since darlist runs were nade.
To evaluate the effects of degraded core accidents on the Sequoyah containment, a small break LOCA with the concurrent icss of emergency core cooling (S2 D) was chosen as the base case. The S2D event is the most probable sequence, resulting in core degradation at Sequoyah. Failure in safety-related systems other than the ECCS was not considered, at the SD2 scenario defines the failures and the probability of those failures. The assumption of additional failures would change the scenario being considered. A review of other probable scenarios shows the SD 2 transient results in more than twice ts much hydrogen generation prior to core slump than was found in the other scenarios. Because of this, using the S2D scenario is a conservative approach for events r e p r e s e n t a t iv e of TMI type of accidents and as a base l case for Sequoyah.
Base Case Assumotions The base casa evaluation provides a conservative appsalsal of the containment pressure and temperature response to this accident. Values for parameters such as hydrogen concentration required to initiate combustion burn completeness, and flame speed were chosen to maximize the containment pressure and temperature. The base case conservatively assumed that a hydrogen concentration of 8 v/o J
ras requir?d to initiate combustion and 85 percent of the bydrogen burned. Test data, including data from Fenwal, as well as literature on combustion, shows that ignition will actually ocent around 5 v/o in a postarcident containment environment with a burn completeness in the 30- to 40 percent range. At 8 v/o the associated adiabat.ic flame temperature is about 1400*F, which is much higher than an adiabatic flame temperature of 800*F at 5 v/o. The assumed burn completeness further increases the energy input rate to the containment.
The 8 v/o-85 percent assumption therefore represents a substantial conservatism. The burn times chosen for each compartment were based on a flame speed of 6 ft/s, assuming ignition occurred at all igniters simultaneously. The flame speed chosen is conservatively high. Information provided by Messrs. Lewis and Karlovitz g iv e the turbulent flame speea of an 8 v/o mixture te be between one and three ft/s. Using the higher flame speed would allow for less heat removal by the ice condenser and contairm.nt sprays, further increasing the calculated pressures and temperatures. The assumption of simultaneous ignition at all igniters in a compartment is also c o n s e rv a t iv e . Even though the containment is well mixed, small variations in hydrogen concentrations throughout a coupartment w ill exist. Ignition may occur at one or two locations initially but probably not at all locations simultaneously. The assumption made in the analysis will increase the energy addition rate, resulting in higher calculated pressures and temperatures. Other containment parameters are modeled to be representative of the plant configuration.
Model A schematic diagram of the containment model for these analyses is g iv e n in Figure 1. Input parameters for the analyses include data for the mass and energy releases from the primary system, burn parameters, compartment initial conditions, flor path parameters, ice condenser door parameters, air teturn fan and hydrogen stimmer system parameters, spray system parameters, and passive heat sink dats.
Data for the mass and energy releases from the primary systen, Tables 1 through 3, are the same r. s those used in previous Sequoyah hydrogen transient analyses, reference 2.
These scenario dependent paraneters include time dependent steam / water mass and energy release rates, hydrogen release rates and temperatures, and fission product energy release rates. The values in Tables 1 through 3 were based on calculations performed by Battelle Memorial Institute Columbus using the MARCH computer program, reference 3.
Burn parameters, Table 4, include the hydrogen volume sA
i fraction required for ignition,.the hydrogen volume fraction
~
required for. propagation of a burn from an adjoining compartment, the fraction of hydrogen burned, the minimum >
fraction required for Ignition, the minimum oxygen volume fraction required to support combustion, and the burn time.
A complete set of burn parameters is provided for each compartment in the model. 'The burn parameters are interdependent, case specific parameters based primarily on experimental data. Values for the oxygen parameters were not varied in these calculations. The oxygen parameters are the standard values used in previous calculations.
Parameters for compartment initial conditions are given in Tables 5 and 7. Values for compartment net free gas volumes and initial temperatures are based on the TMD and LOTIC models for the Sequoyah Final Safety Analysis Report (FSAR),
except the ice condenser temperature which is limited to a minimum value of 32*F in the CLASIX program. The initial oxygen, nitrogen, and steam partial pressures were calculated frca compartment temperatures, pressures, and reistive humidities provided for the LOTIC model discussed in the Sequoyah FSAR, assueing the containment atmosphere-consists of a mixture of stand 0rd air and steam. The 2 million pound-initial mass of ice in the ice bed was specified by TVA. The initial ice heat transfer ares was calculated from values in the TMD model for the Sequoyah FSAR. A value of 248 BTU /lba was used for the heat of fusion of ice to account for both 150 BTU /lba to melt the ice and 98 BTU /lbe to raise the resulting water t e m p'e r s t u r e from 32*F to 130*F. The 130*F water temperature is the Westinghouse NTD-recommended value for the ice condenser drain temperature.
There are five flow paths in the Sequoyah CLASIX model:
lower compartment to ice condenser lower plenum (LC-LP), ice condenser lower plenum to ice condenser upper plenum (LP-UP),
ice condenser upper plenum to upper compartment (UP-UC),
upper compartment to lower compartment (UC-LC), and dead-ended region to lower compartment (DE-LC). Flow loss coefficients and burn propagation delay times for each flow l
path are g iv e n in Table 6 along with minimum flow areas for
[ the paths that do not contain doors. The flow area and loss l coefficient for the UC-LC fl ow path are the Sequoyah FSAR l values for the known flow path through the upper compartment drain holes.
l The remaining loss coefficients and the flow area for the DE-LC flow path were calculated from values in the TMD model for
. the Sequoyah FSAR. For all paths, the burn propagation delay time was calculated by assuming an ignition point in the
! lower compartment or in the ice condenser upper plenum, determining an average burn Icagth to the adjoining compartment, and assuming a f .' a m e propagation at the flame l
l i
I l- speed of interest.
The ice condenser door parameters input to CLASIX are given in Table 8. These include the m a x im um opening angle, the minimum differential pressure to achieve maximum opening, and the ~ door bypass flow area. For the top deck doors, there-is also a minimum differential pressure required to-initiate door opening. Since the scenario considered here is a small break 1 css of coolant accident, it is assumed that the lower inlet door shock absorbers restrict.the maximum lower door opening angle.to 55 degrees throughout the transient.
The Sequoyah containment has two air return fan trains ~with one fan in each train. Each fan takes suction from the upper compartment for the air ret e function and also takes suction from the dead-ended region for a hydrogen skimmer function. CLASIX input parameters for the Sequoyah air return fan and hydrogen skimmer systens are.given in Table-
- 9. Both trains were assumed to be operational. Fan flow was initiated ten minutes af ter the containment pressure reached 3 lb/insg and continued through the end of the transient.
The air return and hydrogen skimmer fractions per fan were based on data in the LOTIC model for the Sequoyah FSAR. Fan head / flow curves were provided by TVA.
The Sequoyah spray system provides spray in the containment upper compartment. Spray system parameters input to CLASIX include the spray-drop diameter, the drop fall time,'the drop film coefficient of heat transfer, and the spray flow rate and temperature. The spray parameters used in these analyses are given'in Table 10. The drop diameter, drop fall time, drop film coefficient, and spray temperature are standard values used in previous calculations. The spray flow rate represents operation of both trains of the coe.tainment. spray system. Spray was initiated 30 seconds after the containment reached 3 lb/in sg and' continued uninterrupted through the remainder of the' transient.
Passive heat sink da ta for the Sequoyah analyses are given in Tables 11 through 16. Table 11 contains compartment-dependent passive heat sink parameters which, for these analyses, are the initial wall temperatures and'the radiant heat transfer beam lengths. Initial wall temperatures were based on values in the LOTIC model for the Sequoyah FSAR.
Radiant heat transfer beam lengths were calculated from general geometry considerations and ice condenser containment dimensions. Table 12 contains material-dependent passive heat sink parameters. These include the emi s s iv i ty, thermal conductivity, volumetric heat capacity, and wall layer-exit heat transfer coefficient for all walls other than those in the ice condenser lower rienum. Standard textbook valuee ---
were used for the material emissivities. Values for thermal
r P
c onduc t iv itie s and volumetric heat capacities were taken~from
- data in the Sequoyah FSAR. Layer exit heat' transfer coefficients were based on values used in the LOTIC model for '
the.Sequoyah FSAR. The last layer of each wall was treated as adiabatic..
Tables 13 through 15 contain specific data for i nd iv idu a l . ,
heat sinks in the upper compartment, lower compartment, and.
dead-ended region, r e s p e c t iv e ly . . These data include surface areas, layer materials, and layer thicknesses, all of which are basedlon data in the Sequoyah FSAR. These' tables also include the numberlof layers per wall and the number of node s -
1 per layer, both of which are based on values used in the
- LOTIC model for the Sequoyah FSAR. . Table 16-contains specific data for individual heat sinks in the ice condenser These data include ' wall surface areas, initial
~
l lower plenum.
wall temperatures, emissivities, the number of' layers per.
wall, the layer thicknesses, layer thermal conductivities,
. layer heat capacities, and lower exit heat transfer coefficients. Values for 211 parameters, except emissivity, were based on values in the LOTIC model for the Sequoyah
- FSAR. Standard textbook values were used for the emi s s iv i t ie s .
i Base Case Transient Results
[ The results of this base case are summarized in Table 17.
l Plots of compartment temperatures, pressures, .and hydrogen volum e fractions for each compartment are given in Figure 3 L through 34.
! Burns occurred both in the ice condenser upper plenas and in
! the lower compartment. In this case, the first buen occurred in the ice condenser upper plenum between 4500 and 4600 seconds into the transient. After the first burn, there was a period during which upper plenum burns vere intermixed with lower compar ment burns at variable inte:rals. During some of the' lower compartment burns, there were concurrent upper plenum burn. During the last phase of this transient, upper plenum burns occurred at nearly constant intervals. In this case, peak hydrogen concentrations in the lower plenum and the dead-ended regions were within 0.5 vol % of the specified ignition points. The peak hydrogen concentration in the upper compartment was one or more percent by volume below the specified ignition point.
The peak calculated containment pressure was 19.0 lb/in g.
This occurred in the lower compartment and dead-ended l
regions. In general, each burn resulted in a rapid pressure l rise throughout the containment and an almost equally rapid l return to approximately the preburn pressure.
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The peak calculated containment temperature was 1245'F. This occurred in the lower compartment.- In general, each burn is characterized by rapid temperature rises of varying magnitudes throughout the containment. After each burn, compartment temperatures return approximately to their preburn values. Exceptions to this general characterization occur in the lower compartment and in the ice condenser lower plenum. For lower compartment burns, the lower compartment temperature returns to slightly higher than preburn values.
For the calculated series of burns, the net effects were lower compartment temperature rises of about 20*F. For ice condenser upper plenum burns, the upper plenan pressurizes relative to the lower plenum and lower compartment. This causes the ice condenser intermediate deck and lower inlet doors to close. With these doors closed, the lower plenum becomes a dead-ended region with a large ice heat sink and very little inflow through the intermediate deck door bypass area. During these burns, significant. cooling occurs in the ice condenser lower plenum and the lower plenum temperature drops about 5'F.
Best Estimate Transient Resnits The base case analyzed is a conservative appraisal of the containment response to hydrogen burns. Table 17 also includes the results of a best estimate case for comparison where the ignition criteria is six v/o with a 60 percent burn completeness. The flame speed chosen'was three ft/s. All other input parameters were identical to the base casa. The best estimate case results in peak containment pressures below the containment design pressure of 12 lb/in 8 g.
Summary The calculated pressures for the base case are close to the design pressure of the containment and well below its ultimate capacity. Some calculated temperatures are above the design basis, but these high temperatures are brief in duration and lower than previously calculated with the earlier version of CLASIX which did not consider heat transfer to structural heat sinks. The effects of hydrogen burns on equipment are discussed in the equipment survivability responses provided to NRC in TVA's response to the August 27, 1981 letter from E. G. Adensan to H. G. Parris.
-- __.____ _ _ _ _ _ _ _ _ _ _ _ _ _ _ . _ _ _ _ _ _ _ ____m_,_ . _ _ _ _ _ _ . _ _ _ _ _ . . _ _ . _ _ _ _ _ , . . _ _ _ _
B. S2D Sensitivity Runs A series of sensitivity runs were made to evaluate the impact and-importance of various parameters on the containment pressure and temperature response to an SD 2 transient.
Factors being considered included fans, sprays, flame speeds, ignition concentrations, and burn completeness. Figure 2 provides a matrix of the cases studied. Other containment and burn parameters and the CLASIX model used were the same as discussed in the base case analysis.
Rennits There are a few general observations that can be made and are applicable to all csses. In no instance was a hydrogen burn precluded either as a result of oxygen depletion or due to high steam concentrations. The calculated containment pressures were always well below the ultimate capability of the containment and generally close to the 12 lb/in8g design pressure.
The first s e n s i t iv i ty case (IA) was run assuming one air return fan and one spray train were operable. This case results in eight burns in the lower compartment and 22 burns in the upper plenum. The peak temperatures and pressures are very s im il a r to those seen in the base case analysis. The results are summarized in table 18. Because no burns occur in the upper compartment, changing the spray flow has very little effect on this case. Case II was run showing the
-ffect of reduced spray on an upper compartment burn.
The second s e n s i t iv i ty case (IB) assumed hydrogen combustion at 10 v/o with a burn completeness of 100 percent. Based on these assumptions, 40 burns occurred in the upper plenum.
Burns did not occur in any other compartment. The peak lower compartment temperature was 214*F. The results are summarized in Table 18.
The third sensitivity run (IC) assumed hydrogen combustion at 6 v/o, with a burn completeness of 60 percent. Nineteen burns occurred in the lower compartment and 36 burns occurred in the upper plenum. Maximum temperatures experienced were 800*F or less in each region of the containment. Results are provided in Tab 13 18.
Sensitivity case 4 (1D) ves the same as the base cese, except the burn completeness wa* !ncreased from 85 to 100 percent.
There were six burns in the lower compartment and 24 burns in the upper plenum. Peak temperatures were approximately 1450*F. Results are provided in Table 13.
- The fifth sensitivity run (IEl assumed hydrogen burn criteria 1
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in the upper and dead-ended compartments of ignition at 6 v/o and a 60 percent burn completeness. Other containnent compartments used the 8 v/o-85 percent burn completeness assumed in the base case. Three burns were found to occur in the lower compartment, 27 burns in the npper plenum, and four burns in the upper compartment. The peak temperature in the upper compartment was less than 500*F. The peak pressure was 19.0 lb/in8g as a result of the upper compartment burns.
Results are provided in Table 18.
In the sixth sensitivity run (IF), combustion was assumed to occur at 6 v/o with a 60-percent completeness, except for the upper compartment where the burn parameters were 4 v/o 40-percent completeness. 'There were 12 lower compartment burns, 25 upper plenum burns, and 8 burns in the upper compartment.
The peak upper compartment temperatures were less than 3158P, and the containment pressures were 13.5 lb/in*g or less.
Results are summarized in Table 18.
In the seventh sensitivity run (IG), the flame speed was reduced from six ft/m to one ft/s. There were six burns in the lower compartment and 26 burns in the upper plenum. The peak temperatures a.sociated with each burn were much lower than in the base case due to the slower energy addition rate, allowing more h'e a t to be removed by the ice condenser and heat sinks. The peak temperatures in the lower compartment and upper plenum were less than 900eF and 1050*F, respectively. The r e s n '. t s are provided in Table 18.
The eighth case (1H) was run assuming a flame speed of 12 ft/s and, as in all cases, simultaneous ignition at all igniters in a compartment. This assumption resulted in six lower compartment burns and 31 burns in the upper plenum.
The peak temperatures in both compartments where burning occurred were approximately 1300*F. The containment pressure was 24 lb/in sg. Results are provided in Table 18.
l The ninth sensitivity case (II) assumed one fan and one spray l
and hydrogen burning at 6 v/o 60 percent in the upper and
- dead-ended compartments to evaluate the sensitivity of spray and fan flow on upper compartment burns. This resulted in six lower compartment burns, 21 upper plenum burns, and two i upper compartment burns. The maximum upper compartment l temperature was 606*F and the containment pressure was l approximately 18 lb/in8g. Results are provided in Table 18.
l The tenth sensitivity case (1J) was used to evaluate the i effects of Isrge quantitles of hydrogen bypassing the upper picnum igniters without being burned. This analysis was done is support of our response to question 14 and was detailed in l
Results are provided in Table 18. $
l that response. -
t i
F The eleventh sensitivity case (1L) assumed a flame speed of three ft/s. The peak containment pressure was 15 lo/8.u8 r, resulting from a lower compartment barn. The peak temperature was 12008F, occurring in the upper plenum.
Results are summarized in Table 18.
The twelfth case (IM) was set up to study the consequences of preventing a burn in the lower compartment under any circumstances. This was accomplished by setting the concentration of hydrogen nr,cessary for Ignition or propagation to 99 v/o. This assumptiot resuited in 47 upper plenum burns. Nine burns propagated from the upper plenum of the ice condenser to the lower plenum. No burns occurred in the upper compartment or dead-ended compartment. The peak containment pressure was 11 lb/in 8 3 Resultrs are included in Table 18.
The thirteenth case (1N) assumed that all ice'was melted when hydrogen was first released to the containment. The burn data was six v/o-60 percent complete in the upper compartment and eight v/o-85 percent complete elsewhere. F iv e burns were predicted to occur in both the lower and upper compartment, resulting in a peak containment pressure of 27.5 lb/in 8 g.
Results are summarized in Table 18.
Additional CLASIX sensitivity runs were submitted in the Sequoyah Nuclear Plant Core Degradation Program Report, Volume 2, Appendix U. These runs were made with an earlier version of CLASIX without heat sinks and the upper plenum node. Still, the older runs provide additional insight into the relative importance of various parameters.
i 9
. _ _ . -~.
C. Scenarios As discussed previously, the base case degraded core event was the S2 D event which.the PHMS effectively mitigates, assuming core cooling is restored prior to core slump. The PHMS will mitigate the effects of a spectrum of accidents, and the discussion presented below represents TVA's approach to determining a range of accidents for which the PHMS will work and the results of our studies.
The approach taken by TVA-was to set up criteria for conditions in the containment that result from the use-of the PHMS and determine mass and energy releases that cause those
- limits to he reached. This approach has several advantages, the first of which is~ it provides a limit to which TVA is confident that PHMS operation is acceptable. Second,.it does not depend on MARCH or s im il ar codes es a principal ba:is for the acceptability of the system. [These criteria do act
.necessarily encompass all events the PHMS may mitigate. It is also porsible to hypothesize events which the PHMS will not mitigate.]
The first criteria was that the event was terminated prior to core slump. Second, the steam concentrations in the lower compartment w ill be below levels where inerting would occur when hydrogen was present. Third, the hydrogen combustion rate will not cause oxygen inerting in the lower compartment. Last, the containment and essential equipment w il l not be damaged to the extent that the plant cannot be j shut down once the ECCS restarts and an uncontrolled release of fission products to the environment does not occur. It 1'
will also be shown that these criteria provide a system that will handle a large range of scenarios with marg 8ns against the containment capabilities. These criteria also reduce the
- number of issues for which there is little experimental data but a wide d iv e r g e n c e of expert opinion.
- The CLASIX code was used to analyze the containment
. response. The physical containment features were the sane as
, used in the S2 D be se case. Ignition of hydrogen was
} assumed to occur sinaltaneously at all igniter locations in a compartment to maximize the pressures and temperatures response of the containment. Hydrogen burn parameters chosen were 8 v/o-85 percent in the lower comp'artment'and ice condenser upper plenum and 6 v/o-60 percent in the upper
- compartment. The location of igniters at a number of elevations in the upper conpartment is the basis for using the lower f l amm ab il i ty limits in the upper compartment. A flame speed of six feet per second was chosen for these cases. As discussed earlier, this is an upper bound flame speed for an 8 v/o hydrogen mixture in a very turbulent. - - - . . -
atmosphere.
I b
'The first' analyses were run using constant steam and hydrogen blowdowns to determine the blowdown rates at which inerting of the lower compartment would occur. A constant blowdown of 0.5 lb/sec hydrogen and 100 lb/sec steam would result in the
. lower compartment steam-concentration reaching 55 percent.
This was considered the maximum acceptable steam flow, as literature presently gives a value of 60 percent as the volume fraction required for steam inerting. A blowdown where the steam flow was maintained at 30 lb/seu and the hydrogen flow rate was 3.5 lb/sec would result in oxygan inerting the lower compartment as a result of burns.
The S2 D hydrogen blowdown was normalized so the peak release rate was three times the value used in the base case (Table 19). For conservatism, the steam releases were not r changed as sdditional steam would act as a burn heat sink.
The results of this case (case 3A) were 14 lower compartment burns, two burns in the upper plenum and one burn-in the upper compartment. The peak pressure was 19.4 lb/in8g.
This case was run again, assuming that all the ice melted prior to the release of hydrogen (case 3B). This resulted in 11 lower compartment burns and one burn-in the upror compartment. The containment pressure for this case was 27 lb/in8 g. This bounds events in which the hydrogen release mighi not occur .ntil after ice melt. Even in this case, the calculated containment pressures are far below the containment's yield strength.
Two other runs were made assuming a six lb/sec hydrogen spike on a modified S 2D blowdown (table 20). One case wa= run assuming ice was present (3C) and the second (case 3D) assumed no ice was present when hydrogen was released to the
( containment. Case 3C resulted in 14 lower compartment burns, l one upper plenum burn, and one burn in the upper l compartment. The peak containment pressure was 17 lb/in 8 g.
! The results of case 3D were similar to those in case 3B with j no ice. The peak containment pressure was found to be 25.2 j lb / in 8 g . Results are summarized in Table 21.
In addition, MAR 06 a naly se s of a numLer of transients were
[
reviewed to compare the mass and energy release retes with those used in this study. The scenarios reviewed include an l intermediate' break LOCA with a loss of ECCS (SI C), a small break LOCA with a loss of containment heat removal (S2 0), a transient loss of main feedwater and loss of all ac power I (TB B2), and a transient loss of rain feedwater, loss of auxiliary feedwater, and loss of the ECCS (TBLD).
l The peak hydrogen and peak steam release rate, when hydrogen is being released, are listed below for each event.
i l
l L _ s
Steam (1b/sec) Hydrogen Ib/sec SD 1 27 1.3 S2G -
No hydrogen produced in 120,000.sec TBB2 17 0.06 TB LD 20 0.048 SD 2 48 1.1 Sensitivity Run 3A 48 3.2 Sensitivity '
Run 3C 48 6.0 As can be seen, the TVA containment studies discussed above considerably bound the release rates for these other scenarios. Further, not only the rate but the total amount of hydrogen released was larger than was produced in the events revieweJ. The steam release rates produced in nach of these events, except for the initial reactor vessel depressurization due to a break, are well below the 100 lb/sec needed to steam inert the lower compartment. The steam releases during the initial blowdown period are not of concern, as the steam is condensed in the ice condenser before hydrogen production due to clad reaction begins. '
Additionally, the core reflood studies discussed in the following section show that the steam and hydrogen release rates are well below the bounds considered in these analyses.
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D. fore Recovery The PHMS was designed to mitigate de' graded core events which are terminated. prior to core slump. The ECCS is therefore assumed to restart before maj or geometrical changes occur in the core. The potential for a maj or steam and/or hydrogen release as the ECCS water enters the hot core has been addressed by three independent methods of analysis.
MARCH runs were made, turning the ECCS on. Westinghouse performed analysis using WFLASH and LOCTA. Hand calculations were made assuming an initial core temperature and determining the flow rates necessary to first quench and then continue to cool the fue?..
The results from all approaches showel little impact on either the steam or hydrogen flow rates. The MARCH runs and the Westinghouse analysit showed peak hydrogen flow rates of less than 1.0 lb/sec and a steam flow rate of approximately 30 lb/sec. The value for the hydrogen rate is within the release rates used.in the SD 2 transient. A 30 lb/sec steam release vould only result in approximately . 20 v/o concentration of steam in the lower compartment. The hand calculation generated an initial spike of 60 lb/sec steam not seen in the more sophisticated computer analysis and a steady steam flow of 33 lb/sec. Summarizing, the hydrogen and steam release rates for ECCS core recovery are similar to the SD 2 base case blowdown and are much lower than those considered i in the blowdown sensitivity studies. Steam or oxygen inerting of compartments w ill not occur for the reflood release rates. These release rates will not result in containment temperatures and' pressures greater than those already presented here or in sections B and C.
J G
A
E. Conclusions Containment anelyses have been performed which evaluate the performance of the PHMS for a wide range of events. Based on this evaluation, criteria for the application of the PHMS have been established. The resulte show that using best estimate assumptions, the design pressure of the containment would not be exceeded for a number of the more probable events resultisg in hydrogen production. Canservative assumptions such as no ice and high hydrogen release rates do not seriorsly challenge the containment ultimate pressure capacity. The peak calculated pressure under all assumptions presented here is less than 28 lb/in8 3, even considering burns in the upper compartment. Steam and oxygen inerting 3
are not found to occur, and the mass release rates associated with core recovery are well within the PHMS functional limits. Therefore, we conclude that the PHMS i s an effective method to mitigate TMI-like degraded core accidents.
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- g - = m.rg g e. ya,3, --w,.p-y-ygw+-g- s-~-9 ,-wi+.39pw..,w-,.,-,w,,u.aw.p. g ,--y,- p_.em., -h...g.e g-%,-yi
REFERENCES
- 1. The CLASIE Computer Program for the Analysis of Reactor Plant Containment Response to Hydrogen Release and Deflagration, OPS Report No. OPS-36A31 (Non-Proprietary); OPS-07A35 (Proprietary)
- 2. Sequoyab Nuclear Plant Core Degradation Program, Volume 2, Report on the-Satety Evaluation of the Interim Distributed Ignition System, December 15, 19F0
- 3. NUREG/CR-1711, MARCH (Meltdown Accident Peeponse Characteristics) Code Description and Users' Manual, October 1980 a
i+
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TABLE 1
. Sequoyah CIASIX Input W ,', '
MARCH Reactor Coolant Mass and Energy Release Rates 1
S2D Secuence Time H2 O Mass Release Rate H2 O Energy Release Rate (seconds) (lbn/sec) (Btu /sec) 0.0 197.2 1.167 x 10 5 2172 190.5 1.097 x 10 5 2478 44.85 5.230 x 10 4 3180 53.53 6.547 x 10 4 3804 34.82 4.262 x 10 4 4428 21.40 2.842 x 10 4 4752 48.42 5.558 x 10 4 5700 19.42 2.182 x 10 4 6012 14.07 1.583 x 10 4 6960 5.253 5.989 x 10 3 7062 4.718 5.388 x 10 3 7206 4.060 4.693 x 10 3
~.
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TABLE 2
. . Sequoyah CLASIX Input
[,;.u;;.
MARCH Hydrogen Generation Rates and Temperatures S2D Seq..ance Time H7 Mass Felease Rate H Temperature 2
(seconds) (lam /sec) (F) 0.0 0.0 61 3480 0.0 61 3804 0.0413 67 4116 0.260 1582 4428 0.740 795
~
4752 1.07 771 5700 0.430 612 6330 0.223 555 6648 0.160 535 6960 0.117 519 8070 0.0367 519 L
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TABII 3 Sequoyah CIASIX Input j
(:o v' MARCH Fission Product Energy Release Rates
- 1 4
S2D Secuence 4 Time Energy Release Rate (seconds) (Btu /sec) 1 0.0 0.0 h 3810 0.0 4116 1803 - 4428 4800 ; 4752 6703 - 5376 7000 7080 '7135 t N 4 i.:.
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f Sequoyah CIASIX Ingxst
.) Compartment Initial Condit.lons j -
a 1
'i tower Ice Condenser ice Con-Jenser Upper Dead Ended
'j Compartment lower Plenum Upper Plentn Compartment Itegion
~
3
$ Volume (f t ) 289000 24200 47000 651000 94000 1
j Temperature (F) 100 32 32 85 100 9 0 Pressure (psia) 3.12 3.1? 3.12 3.12 3.12 2 N Pressute (psia) 11.78 11.78 11.78 11.81 11.78 2 1I 0 Pressure (psia) 0.09 0.09 0.09 0.05 0.09 7
^4 4
4 4
TABLE 6 Sequoyah CM SIX Input Flow Path Parameters If-LP LP-UP UP-DC UC-LC DE-I.C 2 ** ** ** Minimum Flow Area (f t ) 2.2 298 Flow Loss Coefficient
. 0.89 1.04 1.43 1.5 4.2 Burn Propagation Delay Time (sec)* 2.5 5.4 2.7 8.0 3.2 i
J
- Based on a flame speed of 6 ft/sec.
** Function of door opening.
I tt I " ? Y* Y**' " " - - - '. ', stW -, y . . . , . 77.'9,1-Q-f *, ' " ' ' * *, ' ' *
- f ',3'E .*M *-
3 1 -
. * = . 'f ,' l T'
TAB?2 7 l
.. Sequoyah CIASIX Input !
E. ., Ice Bed Parameters , Parameter Value " 6 Initial Ice Mass 2.22 x 10 lbn - 5 2 Initial Ice Heat Transfer Area 2.68 x 30 ft Heat of Fusion of Ice 248 Btu /lbn* Flow Loss Coefficir.t 0.0 - Initi.21 Net Free Gas Voltrae 86300 ft 3 , Includes 150 Btu /lbn actual heat of fusion plus 98 Btu /1tra to raise ice . condenser drain temperature from 32 F to 130 F. e P7". M- .,-r, m -. N, T.- ,, - , 7?W, - -
- , - ' - - P. -
- -. - N,.-- # ;-'-g""* W
1 TABLE S Sequoyah CMSIX Input Tce Condenser Door Parameters Lower Inlet Doors I Maximtra Opening Angle 55 ! Minimtrn Differential Pressure for Maximum Opening 0.0206 psi ! Maximtra Flow Area 840 ft Bypass Flow Area O Intermediate Deck Doors Maximtra Opening Angle 89 Minimum Differential Pressure for Maximum Opening 5.5 psi Maximtra Flow Area 2 982.5 ft Bypass Flow Area 2 20 ft , Top Deck Doors '
- Maximum Opening Angle 89 Minimitn Differetuial Pressure for Maximum Opening 1.15 psi Maximtra Flow area 2003 ft 2 Bypast, Flow Area 2 20 ft Minimtra Differential Pressure to Initiate Door Opening 0.005 psi pyg _ am,, ,*WW- ~v~ '." '" -
>C * "~ ^ UN'?
~
'--'T- +
TABLE 9 Sequoyah CLASIX Input Air Return Fan /Hvdrocen Skinrner System Parameters Parameter Value Number of Trains 2 Initiation Time 712 sec* Air Return Fraction per Train 0.9945 Hydrogen Skimmer Fractirn per Train 0.0055 Flow Rate Fead Flow Rate Per Train (in H 2O) (cfm) 0.0 5.80 x 10 4 0.85 5.80 x 10 4 2.00 5.35 x 10 4 3.00 4.85 x 10 4 4.00 4.20 x 10 4.25 4.00 x 10 4 4.50 3.80 x 10 4 4.75 3.50 x 10 4 5.00 3.10 x 10 4 5.20 2.75 x 10 4 5.20 0.0 t l
- Initiated 10 minutes af ter the containment eaches 3.0 psig pressere.
l l l
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J TABZI 10 Sequoyah CIASIX Input c:. Spray System Parameters 1 1 Parameter Value Drop Diameter 0.0268 in Drop Fall Time 10 see Flow Rate 9500 gpn Temperature 125 F Drop Film Coefficient 20 Btu /hr ft2 7 Initiation Time 142 sec* s, . 4
- Initiated 30 seconds after the containment reaches 3.0 psig pressure.
~
*/ ; . "',TA,*k*,M'-
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%T f% ', p W , " 4.,,y ] 7, ' / f g -- -, , y ; : Wl' = - ~ ~ f_7= sT"P"*' j >=~q *M'*""-
_ _ : ' "' ^: . '
a k 1 e TABLE 11 a i Secuoyah CIASIX Input q M, Compartment Dependent Passive Heat Sink Parameters i Parameter Compartment Value l 3 J Temperature Lower Compartment 100 F } 1 Ice Condenser Iower Plena
- i Ice Condenser Upper Plens ;
t Upper Compartment 85 F ' Dead Ended Region 100 F Radiant Heat Transfer Lower Compartment 59.0 ft Beam Length Ice Condenser Lower ?lentn 8.5 ft Ice Condenser Upper Plenum 8.5 ft** Upper Compartment 59.0 ft Dead Ended Region 8.5 ft i I
*See individual lower plenum wall data in Table 16.
**There are no walls in the upper plenum in this analysis.
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.s
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, - , .,- -- n , , . -,
TABLE 12 Sequoyah CIASIX Input Material Dependent Passive Heat Sink Parameters
- Parameter Material Value Danissivity Concrete 0.9 Carbon Steel 0.9 Coating 0.9 Therual Conductivity Costing on Steel (OC) 0.21 (Stu/hr f t F) Coating on Steel (LC, DE) 0. 22 Coating on Concrete 0.087 Concrete 0.84 Stainless Steel 9.87 Carbon Steel 27.3 Volumetric Heat Capacity Coating on Steel (UC) 29.8 3
(Bta/ft F) Coating on Steel (LC, DE) 14.7 Coating on Concrete 29.8 Concrete 30.2 Stainless Steel 59.2 Carbon Steel 59.2 Exit Heat Transfer Coefficient 4 Coating to Steel or Cencrete 10 2 8 (Stu/hr ft F) Concrete to Concrete 10 Steel to Concrete 10 0 Steel to Steel 10 Last Layer Adiabatic Wall 0
*For ice condenser lower plentzn walls see individual wall data in Table 16.
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TABLF,13 i Sequoyah CLASIX Input Upper Compartment Passiva lleat Sinks
.j .
,, CLASIX Wall Surface Layer Number Layer Layer {
,l Number Description Area (ft ) Number of Nodes Material *Ihickness (f t) l
-4 1 Part of containnent shell 52457 1 2 coating 6.5 x 10 and iciscellaneous steel 2 3 carbon steel 0.042
-4 2 Part of containment shell 2373 1 2 coating 6.5 x 10 and miscellaneous steel 2 10 carbon steel 0.1264 3 Part of the operating deck 4032 1 3 stainless steel 0.0217 0.4 d 2 20 concrete 3 20 concrete 0.4 x
4 20 concrete 0.4 5 20 concrete 0.4 i 4 Part of the operating deck 5124 1 20 concrete 0.4 2 20 concrete 0.4 3 20 concrete 0.37 i ! -4 Part of the operating deck 19992 1 2 coating 5.56 x 10 5 2 10 concrete 0.2 j j 20 concrete 0.4 3 i 4 20 concrete 0.4 5 20 concrete 0.41 l
- h 3
~
.t
] '
s j TABLE 14 Sequoyah CIASIX Input Lower Compartment Passive IIcat Sir.ks CLASIX Wall Surface 2 Layer Humber Layer layer ' -; Ntaber Description Area (ft ) Ntuber of ikxles Material Thicknes.2 (ft)
-4 6 Miscellaneous steel 12915 1 2 coating 6.5 x 10 2 15 carbon steel 0.221 3 15 ca-bon steel 0.W1 7 Part of interior concrete 2304 1 3 stainless steel 0.0217 2 20 concrete 0.5 3 20 concrete 0.5 4 20 concrete 0.5 5 20 concrete 0.6 4
{
! 8 Miscellaneous steel 4200 1 2 , coating 6.5 x 10 2 10 carbon steel 0.1286 l
9 Miscellaneous steel 12810 1 2 coating 6.5 x 10 l cf4 2 5 carbon steel 0.0759 l
- l i 10 Parts of the operating deck, 36748 1 20 concrete 0.4 1 crane wall and interior 2 20 concrete 0.4
! concrete 3 20 concrete 0.4
! 4 20 concrete 0.35 l
-4 11 Parts of the operating deck, 9029 1 2 coating 3.97 x 10 crane wall and interior 2 20 concrete 0.4 concrete . 3 20 concrete 0.4 4 20 concrete 0.4 5 20 concrete 0.35 I
4 4 e
J - m h' > I' TAllLE 15
-5 Sequoyah CIASIX Input I
j- Dead Ended Ilegion Passive Ileat Sinks "tASIX l Wall Suaface 1.ayer Nuraber Layer Layer 2 cj Number Description Area (f t ) Ntznber of Nodes Material ' thickness (f t) 12 Parts of the crane wall 22501 1 20 concrete 0.4 J and interior concrete 2 20 concrete 0.4 l 3 20 concrete 0.58 l 13 Part of the contairunent shell 8085 1 2 coating 6.5'x 10
-4
] 2 10 carbon steel 0.1204 l
-4
]h
-l 14 Part of the containment shell 8610 1 2 10 2 coa t!.. .c, carbon steel 6.5 x 10 0.10 3
'I
) 15 Part of the contairunent shell 3045 1 2 coating 6.5 x 10
-4 2 5 carbon steel 0.065
-4 16 Parts of the crane wall, 12558 1 2 coating 5.25 x 10 containment floor, and 2 20 concrete 0.4 Interior concrete 3 20 concrete 0.4 4 20 concrete C.4 5 20 concrete 0.43 a .
- I J
d I
.d 4
4 0 'e 2 s ,-*e__* e se . 8e.. se f9 2 2 '**:. & 2 no *.4 ? ..A 's, M. IM , f2' ! 2? $ ~ b d ._ ? %0 004 I I.!
- fd j'. # 8A' I* $ -[ ' ' - d *N 'd
-y
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i TNTLE 16 Sequoyah CIMIX Input Ice Condenser Lower Plenum Passive lleat Sinks i CLASIX Layer Layer lleat Layer Exit l Wall Surface Initial Wall Layer Layer Conductivity HeatTransfer 13 Number Area (ft ) Temperature (F) Dnissivity Ntsnber ' thickness (f t) (Btu /hr f t F) Capacity (Btty'ft F) (Bttyhr f t 9 17 19100 80 0.9 1 0.2 0.15 2.75 10 2 0.2 0.15 2.75 10 6 3 0.2 0.15 2.75 10 4 0.4 0.15 2.75 0.7 5 0.0625 26.0 56.4 0.0 18 13055 80 OM 1 0.2 0.2 3.663 10 2 0.2 0.2 3.663 10 6 3 0.2 0.2 3.663 10 4 0.4 0.2 3.663 0.7 5 1.0 0.8 28.8 0.0 l 19 3336 15 0.9 1 8.33 x 10 0.0833 28.4 10 2 0.2 0.2 28.8 10 3 0.13 0.13 28.8 0.0 l. i s , et _ _ _ _ _ _ _______ _
TABLE 17 SEQUOYAH CLASIX S D COMPARISON OF BASE CASE WITH A BEST ESTIMATE CASE 2 Base Case Best Estimate (Y1) (FF1) Number of Burns LC 7 19 UP 30 36 UC 0 0 Magnitude of Burns (1bm) LC 104 56 UP 31 18 UC - - Total H2Burned (lbm) 1092 120' H2 Remaining (1bm) 445 335 Peak Temperature ( F) LC 1705 760 UP - 1220 667 UC 163 146 DE 257 177 Peak Pressure (lb/in2 a) LC 33.4 25.3 UP 27.8 24.1 UC 25.1 23 2 DE 32.8 25.2 Ice Remaining (1bm) 7.83 x 10 5 7.80 x 10 5 Figures 3-34 242-257
~ - - - .--n m =.= -
.,n~n - n ,~nc-_,,,-- -
TABLE 18 SEQUOYAH CLASIX S D PARAMETER SENSITIVIri RESULTS
SUMMARY
2 Case Base Case 1A Case 1B S2D Base (NEWZ} 1 Fan,1 Spray (A3) 10-100 (U1) Number of Burns LC 7 8 0 UP 30 22 39 UC 0 0 - 0 Magnitude of Eurns (lbm) LC 104 97 - UP 31 27 40 UC - - - Total H Burned (lbm) 1092 1094 950 H2 Remaining (1bm) 445 443 587 Peak Temperature ( F) LC 1245 1210 214 UP 1220 1195 1840 UC 163 201 171 DE 257 265 130 Peak Pressuae (1b/in a) LC 33.4 32 3 22.7 UP 27.8 - 30.7 27.3 UC 25.1 26.8 24.4 DE 32.8 31.3 22.7 5 5 5 Ice Remaining (lbm) 7.83 x 10 9.35 x 10 7.82 x 10 Figures 3-34 35-50 51-66 I e
-7 y*l .7MA*W8M an-- ~-~J'F - . , , _ _ _ . , _ - ' , - -
S(-^ , - . , - - - - - - - ---6 PN- - s- ,,,.v_m._ ,4 .
TABLE 18 (Continued) SEQUOYAH CLASIX S D PARAMETER SENSITIVITY RESULTS
SUMMARY
2 Case 1C Case 1D Case 1E 6-60 (T1) 8-100 (02) 6-60 UCDE (C3) Number of Burns LC 19 6 3 UP 36 24 26 UC 0 0 4 Magnitude of Burns (lbm) LC 55 124 105 UP 18 38 30 UC - - 150 Total H2Burned (lbm) 1233 1085 1252 H2 Remaining (lbm) 333 452 285 Peak Temperature ( F) LC 805 1457 1170 UP 678 1469 1234 UC 148 192 504 DE 198 295 258 Peak Pressure (lb/in a) LC 27.5 34.9 33.4 UP 25.6 30.4 27.8 UC 23.6 26.9 30.9 DE 27.0 35.2 32.8 Ice Remaining (lbm) 7.81 x 10 5 7.78 x 10 5 8.02 x 105 Figures 67-82 83-98 99-114
- , - , w--
, _ ,7,y y
' ' ~ , ,
's
..i .} b,w
l TABLE 18 (Continued) SEQUOYAH CLASIX S D PARAMETER SENSITIVITY RESULTS
SUMMARY
2 I Case 1F Case 1G Cass 1H 6-60,4-40 UC Flame Speed = ' Flame Speed = (D3) 1 ft/sec (E3) .12 ft/sec (E3) ; Number of Burns LC 12 6 6 UP 25 26 31 UC 8 0 0 Magnitude of Burns (1bm) LC 58 101 102 UP 20 33 32 UC 68 - - Total H2Burned (ibm) 1296 1086 1092 H2 Remaining (Ibm) 241 451 445 Peak Temparature ( F) LC 759 884 1306 UP 678 1114 1263 UC 314 150 182 DE 205 170 314 Peak Pressure (lb/in a) LC 27.9 24.8 38.2 UP 25 3 24.5 29.2
- UC 25 3 24.3 25.5 DE 27.0 24.8 33 7 Ice Remaining (lbm) 8.07 x 10 5
7.71 x 10 5 7.86 x 10 5
~
Figures 115-130 131-146 147-162
~
1 l [
TABLE 18 (Continued) SEQUOYAH CLASIX S D PARAMETSR SENSITIVITY RESULTS
SUMMARY
2 Case 1I Case 1J Case 1L 6-60 UC&DE 8-40 UP (J2) Flame Speed = 1 Fan,1 Spray 3 ft/see (Y1) (V1) Number of Burns LC 6 9 8 UP 21 38 27 UC E O O Magnitude of Burns (35m) LC 105 97 104 UP 34 22 31 UC 150 - - Total H2Burned (1bm) 1186 1065 1090 H2 Remaining (lbm) 351 472 447 Peak Temperature ( F) LC 1159- 1284 1168 UP 1200 585 1196 UC 606 157 172 264 220 DE 252 Peak Pressure (lb/in a) LC 32 3 32 3 29.6 UP 32.1 27.1 27.3 UC 32.7 25.2 25.8 DE 31 3 31.2 29 1 Ice Remaining (1bm) 9.44 x 10 5 7.85 x 10 5 7.78 x 10 0 Figures 163-178 179-194 195-210
--, .--m--~.---=. -- -,: -v r- -- - -- m,- -
I* A 4- _a- _ _ __ _ , _
TABLE 18 (Continued) SEQUOYAH CLASIX S D PARAMETER SENSITIVITY RESULTS
SUMMARY
2 Case 1M Case 1N 99-85LC(BB1) No Ice,6-60 UC (GG1) Number of Burns IC 0 5 UP 47 0 UC 0 5 Mesnitude of Burns (lbm) LC - 114 UP 29 - UC - 172 Total H2Burned (lbm) 1084 1243 H2 Re:naining (1bm) 453 295 Peak Temperature ( F) LC 214 1132 UP 1228 435 UC 153 548 DE . 128 553 Peak Pressure (1b/it. a) LC 22.5 37.5 UP 25.4 41.6 UC 23 9 41.6 DE , 22.5- 41.8 Ice Remaining (lbm) 7.44 x 10' N/A Figures 211-226 227-241 e G ( wm--
- - . - - - , , -_ --;regrf m a'97.M_W *** ** N 4eLNN,*%NN,f mewsgr* 8{hs , "**+rs_' - *>* N e * ** *="N *Pu*ng*"w Nwe ,"* ? g 7'sS r. " * = "'
- I TABLE 19 ,
BLOWDOWN SENSITIVITY 2 H RATE (3 lbm-H 2
'**" 891**)
Time Flow Tempgrature (sec) (lbm/sec) (7) 3480. O. 61. 3804. 0.1239 61. 4116. 0 7800 1582. 4428. 2.220 795. 4752. 3 210 771. 4770. O. 612. TABLE 20 . BLOWDOWN SENSITIVITY H RATE (6 lta-H /s* spike) 2 2 Time Flow Tempgrature (sec) (1bm/sec) ( F) 3480. O. 61. 3804. 0.1239 61. 4116. C.7800 1582. 4428. E.220 -795. 4620. 2.220 771. 4645. 6.000 612. 4670. 2.220 555. 4795. 2.220 535. 4795. O. 519. p A Saem , - , - --._-.--55' M^----- . , , --
^^
N C - - M ,, %^%-- _T ~_%V.* 9 T M *"yM""****-. PM9 - MN 6" WA6M.W W
. - - . . - . . . . . - , . _. _, -.. -_ . - -, - - . . - _, -e--- . - - - - - - - . _ _ . , - . , , _ , . - - - . . , - - . -- . ~ , ,
/
i TABLE 21 ;
?
SEQUOYAH CLASIX BLOWDOWN SENSITIVITY RESULTS
SUMMARY
i Base Case Best Estimate 3xH 2Rate (JJ1) 3xH 7hate (KK1) [ No Ice ' Number of Burns LC 14 11 UP 2 0
'IC 1 1 F.agnitude of Burns (lbm) LC 67 94 '
UP 16 - UC 149 193 Total H2Burned (1bm) 1268 1177 H2 Bemaining (ibm) 269 360 Peak Temperature ( F) LC 3 78 1493 UP 1216 603 UC 498 546 DE 286 315 Peak Pressure (lb/in a) LC 33.8 41.3 UP 29.6 40.0 UC 30.0 40.8 DE 31.6 40.9 Ice Remaining (lbm) 1.05 x 10 6 N/A Figures 258-273 274-288 F O,,_ ' NEk MMY@_ M* '[ M P O MMa NW
,M.MM %O 7
%6 % h% @.0M g gd f. g gS %.. p g e %9rg g* @g Q-
TABLE 21 (Continued) SEQUOYAH CLASIX BLOWDOWN SENSITIVITY RESULTS
SUMMARY
Base Case Best Estimate
' 3 x H, Rate (LL1) 3 x E, Rate ( 21) 6 1F/see spike 6 lb7see spike, No Ice Number of Burns LC 14 11 UP 1 0 UC 1 1 Magnitude of Burns (1bm) LC 79 96 UP 20 -
UC 148 101 Total H Burned (lbm) 1243 1177 H2 Remaining (1bm) 294 360 Peak Temperature ( F) LC 1340 1310 UP 1206 612 UC 517 542 f DE 266 286 Peak Pressure (1b/in a) LC 31.4 39.6 UP 29.2 39.4 UC 33.5 40.0 DE 29.6 ~3 8.3 6 Ice Remaining (1bm) 1.05 x 10 N/A Figures 289-304 305-319 E71309.03
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"I lM4 ) ", O ,' M - _ . - - . . . - _ _
1 (:j FIGURE 1 SEQUOYAH CLASIX MODEL , 1
,1
?
1
'''* ~
ICE CONDENSER - m UPPER UPPER l PLENUM COMPARTMENT
~
-1 A l l
i ' I ICE BED I g_________, e t Y Y i t ICE '--_W DEAD CONDENSER LOWER LOWER 4 4-4 > ENDED PLENUM COMPARTMENT REGION '
-~~ ---
AIR RETUP.J FAN / HYDROGEN SKIMMER SYSTEM FLOW PATH CONTAINS DOORS
< > SLOW ALLOWED IN BCTH DIRECTIONS l
1 FLOW ALLOWED IN ONE DIRECTION
........... SPRAY HEADER s,ppw MvtM.w --
,3 , y wT < *4N 7
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8 '7 ) -
i FIGURE 2 MATRIX OF S D 2 SENSITIVITY STUDIES Flame Speed 1 3 6 12 Burn Parameters Case 2 Fans 1 Fan 2 Sprays 1 Spray ft/sec ft/sec ft/sec ft/sec LC UP UC DE Base X X X 8/85 8/85 8/85 8/85 1A X X X 8/85 8/85 8/85 8/85 1B X X X 10/100 10/100 10/100 10/100 1C X X X 6/60 6/60 6/60 6/60 1D X X X 8/100 8/100 8/100 8/100 1E X X X 8/85 8/85 6/60 6/60 IF X X X 6/60 6/60 4/40 6/60 10 X X X 8/85 8/85 8/85 8/85 1H X X X 8/85 8/85 8/85 8/85 II X X X 8/85 8/85 6/60 6/60 1J X X X 8/85 8/40 8/85 8/85 1L X X X 8/85 8/85 8/85 8/85 1H X X x 99/0 8/85 8/85 8/85' 1N X X X 8/85 8/85 6/60 8/85
"no lower compartment burns allowed anno ice during fl2 pr duction E71309.05
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