ML20117F281
| ML20117F281 | |
| Person / Time | |
|---|---|
| Site: | Summer  |
| Issue date: | 02/29/1996 |
| From: | Bricenash R, Swamy S WESTINGHOUSE ELECTRIC COMPANY, DIV OF CBS CORP. |
| To: | |
| Shared Package | |
| ML19311C239 | List: |
| References | |
| NUDOCS 9609030414 | |
| Download: ML20117F281 (200) | |
Text
I WESTINGIIOUSE NONcPROPRIETARY CLASS 3 VIRGIL C. SUMMER RESIDUAL HEAT REMOVAL DATA REVIEW AND MONITORING CRITERIA DEVELOPMENT FEBRUARY 1996 i
P. L. STRAUCH Verified by:
N' R. L. Brice-Nash Structural Mechanics Technology Approved by:
't AJAf S.A.Swamy Structural Mechanics Technology 9609030414 960827 DR ADOCK 0500 5
Work performed for South Carolina Electric and Gas Co. under Charge Number SULP-964.
WESTINGHOUSE ELECTRIC CORPORATION Systems and Major Projects Division P. O. Box 355 Pittsburgh, Pennsylvania 15230
@ 1996 Westinghouse Electric Corporation All Rights Reserved Attachment to MSE-SMT-96-031
TABLE OF CONTENTS Section Title Page 1.0 Introduction 1
2.0 RHR Line Layout and Temperature Differences 3
3.0 Finite Element Thermal and Stress Analysis 5
4.0 Temperature Monitoring Criteria Development 9
5.0 Summary and Conclusions 16 6.0 References 17 Attachment A: Temperature Plots from Program WECAN/Plus Al to A3 Attachment B: Stress Plots from Program WECAN/Plus B1to BIS l
4 i
Attachment to MSE-SMT-96-031 i
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1.0 INTRODUCTION
United States Nuclear Regulatory Commission (NRC)Bulletin 88-08 (Reference 1) was issued on June 22,1988 as a result of a pipe cracking incident at Farley Unit 2, and l
subsequent evaluations which confirmed that valve leakage caused the failure. The purpose of the bulletin was to request that licensees review their reactor coolant systems (RCSs) to 4
identify any connected, unisolable piping that could be subjected to adverse thermal stresses, and take action to ensure that piping will not be subjected to unacceptable thermal stresses.
l Bulletin 88-08 requested three specific actions for utilities ir. the United States:
1)
Review systems connected to the RCS to determine whether unisolable sections of piping connected to the RCS can be subjected to stresses from temperature stratification or temperature oscillations that could be induced by leaking valves, and that were not evaluated in the design analysis of the piping. (Unisolable piping sections include the piping between the RCS and the first check valve or isolation valve beyond the RCS).
2)
For any unisolable sections of piping connected to the RCS that may have been subjected to excessive thermal stresses, examine nondestructively the welds, heat-i affected zones and high stress locations, including geometric discontinuities, in that piping to provide assurance that there are no existing flaws.
3)
Plan and implement a program to provide continuing assurance that unisolable sections of all piping connected to the RCS will not be subjected to combined cyclic and static thermal and other stresses that could cause failure during the remaining life of the unit. This assurance may be provided by redesigning and modifying these sections of piping to withstand combined stresses caused by various loads, including temporal and spatial distributions of temperature resulting from leakage across valve seats; instrumenting this piping to detect adverse temperature distributions and establishing appropriate limits on temperature distributions; or providing a means for ensuring that pressure upstream from block valves which might leak is monitored and does not exceed RCS pressure.
Supplement I of Bulletin 88-08 was issued on June 24,1988, following a pipe cracking incident at Tihange Unit 1 in Belgium. This crack was in the base metal of an elbow, and not in the weld or heat-affected zone, as at Farley. The purpose of this supplement was to emphasize the need for sufficient examinations of unisolable piping connected to the RCS to ensure that there are no rejectable crack or flaw indications, and that examinations of high stress locations should include the base metal, as appropriate.
Supplement 2 of Bulletin 88-08 was issued on August 4,1988. The experience at Farley Unit 2 and Tihange Unit 1 indicated that the ultrasonic testing procedures used were unable to reliably detect thermal fatigue cracks in stainless steel piping. Therefore, the purpose of this supplement was to emphasize the need for enhanced ultrasonic techniques and experienced examination personnel to detect such cracks.
Attachment to MSE-SMT-96-031 1
Supplement 3 of Bulletin 88-08 was issued as a result of a cracking incident in the residual heat removal suction piping at a foreign reactor on June 6,1988. This incident was different than the Parley incident, in that this event involved " hot" leakage exiting the RCS, whereas the previous incidents involved " cold" leakage entering the RCS. Also, this event involved periodic leakage through the valve packing gland, whereas the Farley incident involved steady leakage through the isolation valve (upstream to downstream). Therefore, the purpose of this supplement was to alen utilities that periodic valve seat leakage through packing glands could result in unacceptable thermal stresses.
1.1 SCE&G Response to Bulletin Requests South Carolina Electric and Gas Company (SCE&G) has been very responsive to NRC Bulletin 88-08 requests. Identification of susceptible systems and inservice inspection locations is documented in References 2 and 3. Lines which were determined to be susceptible to adverse stresses from valve leakage include the following:
- 6" Safety Injection Lines to the Cold Legs
- 6" Safety Injection Lines to the Hot Legs
- 3" Normal Charging Line 3" Alternate Charging Line 2" Auxiliary Spray Line
- 12" Residual Heat Removal Suction Lines from Loops A and C Hot Legs To address action 3 of the bulletin, SCE&G has implemented temperature monitoring.
Residual heat removal (RHR) monitoring data from 1993 through 1995, along with line layouts and insulation drawings were transmitted to Westinghouse via Reference 4. Per Reference 5, temperatures for the Loop C residual heat removal line are exceeding the current acceptance criteria of 50 F. The top to bottom of pipe temperature differential is approximately 160 F and has been relatively steady for about one year. The Loop A residual heat removal line temperature is approximately 100 F at the top of the pipe, with no significant fluctuations. The temperature at the bottom of the pipe is unavailable, but should be approximately the same as the temperature at the top of the pipe.
1.2 Purpose of Report SCE&G has requested Westinghouse assistance (Reference 6)in evaluating the stratification condition in Loop C and determining why there are differences in the temperature readings for Loops A and C. In addition, temperature monitoring data acceptance criteria for the RHR lines were developed, based on finite element thermal and stress analysis. The acceptance criteria are defined in terms suitable for automated surveillance.
Attachment to MSE-SMT-96-031 2
l 2.0 RHR LINE LAYOUT AND TEMPERATURE DIFFERENCES 4
4 Branch pipes, attached to header pipes containing hot fluid with a large velocity, are heated by eddies which travel from the main header into the branch pipe. This significantly i
influences the temperature distribution in the branch pipe. For branch pipes connected to typical pressurized water reactor (PWR) coolant systems, testing and plant measurements have found [
i
]'".
Turbulent penetration heating of branch pipes may 1
be facilitated by convection heating for pipes which are oriented horizontally or upward from the header pipe.
i Based on the data evaluated in Reference 7, a range of turbulent penetration lengths must be assumed, or the length must be determined by plant measurements. For branch lines which are 3" nominal pipe size or larger, in typical PWR designs, turbulent penetration length
[
]*".
2 The layouts of the Summer RHR lines and the temperature monitoring locations are shown in Figure 2-1 (see References 8 and 9 for piping layout and monitoring locations). As shown,
]
distances from the loop connection to the hoiizontal piping near the isolation valve are about 21 pipe inner diameters for Loop A and about 24 pipe inner diameters for Loop C. (The piping is 12" schedule 140, 12.75" outer diameter,10.5" inner diameter,1.125" thickness, i
SA376 Gr 316 stainless steel). Therefore, the lengths are [
]"". Since the lines are oriented downward from the hot legs, there is no convective heating from the hot leg.
The Loop A and Loop C layouts are therefore essentially the same with respect to turbulent penetration heating, and one wot6d expect similar temperatures in the horizontal piping near isolation valves 1-8702A and 1-8702B. However, the Loop A temperature is approximately ambient temperature, and the Loop C temperature is much warmer (about 360 F at the top of the pipe and 200 F at the bottom of the pipe). The reason for the difference [
]'".
4 j
Attachment to MSE-SMT-96-031 3
(Loop C Hot Leg 3.81' 3.05' 4.39' 3
(Loop A Hot Leg 4.29' 11.56' 1TE10765A(top) 1TE10765B (bottom)
%.52' 2
1-87028 14.21' 1TE10764A (top) 1TE107648 (bottom) 2.83 1-8702A Notes: 1) Piping lengths are to elbow working points
- 2) Elbow radius of curvature is 1.5' Figure 2-1: Virgil C. Summer Residual Heat Removal Suction Piping Layout and Temperature Monitoring Locations I
i Attachment to MSE-SMT-96-031 4
3.0 FINITE ELEMENT THERh1AL AND STRESS ANALYSIS When thermal stratification occurs, the pipe is partially filled with hotter water and partially filled with colder water. In some cases, the transition between the hot and cold water can occur over the entire pipe inner diameter (vertically). In the other extreme, the transition may occur over a relatively short distance, with a very large temperature gradient near the interface. Therefore, the temperature gradient may be linear, a step change or something between these extremes. For the purpose of analysis, [
]'"
Thermal stratification may occur in the horizontal sections of the RHR suction piping near isolation valves 1-8702A and 1-8702B as a result of leakage through the isolation valve packing glands and the leakoff lines. (The horizontal section of piping at elevation 425 feet in RHR Loop C is expected to be hot since it is located [
]'"
from the hot leg connection). Thermal stratification may also occur as a result of [
]'".
Thermal stratification results in global bending stresses due to the temperature gradient from the top to the bottom of the pipe, as well as local stresses resulting from temporal and spatial temperature gradients within the I
P Pe-Thermal cycling will occur if the isolation valve leakage is periodic, or if variations in
[
]'" are sufficient to result in the pipe being periodically stratified and then cold. Thermal cycling results in material fatigue damage, the severity of which is dependant on the stress range, the number of stress cycles, the existence of stress risers and the material.
Thermal striping is a cyclic mechanism caused by instabilities in the hot-cold fluid interface in a stratified loading during relatively steady flow conditions. This mechanism can cause fatigue damage at the interface location under certain conditions of stratified flow, as in surge line stratification during insurges and outsurges. [
]*".
Since the section of piping that may be stratified is relatively short, the stress effects are most significant for components in the horizontal piping immediately upstream of the isolation valve: the elbow, the elbow welds, straight pipe, and the valve inlet weld. The valve inlet weld is judged to be the critical component due to the valve body transition, which is tapered at an angle of 18 degrees (Reference 10). The other components have a constant wall thickness.
A 3D finite element model of the valve inlet weld region was created and analyzed using WECAN/Plus (Reference 11). The model mesh is shown in Figure 3-1. The model was created from 3D isoparametric brick (20 node) and wedge (15 node) elements. Due to symmetry in the model geometry as well as the thermal loading, only one-half of the full circumference was included.
Attachment to MSE-SMT-96-031 5
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Figure 3-1: Valve Weld Region Model Attachment to MSE-SMT-96-031 6
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3.1 Thermal Stratification Thermal Analysis Transient and steady state thermal analyses were performed to obtain temperature solutions for input to transient and steady state stress analysis computer runs. [
]'".
Two step change stratification loadin"s were analyzed. [
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]'".
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The second loading [
]'".
The heat transfer film coefficient between the water and the pipe inner surface was determined by the following equation [
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Temperature plots from the Profile 1 and Profile 4 analyses are included in Attachment A.
Attachment to MSE-SMT-96-031 7
3.2 Thermal Stratification Stress Analysis Using the thermal analysis temperature solutions, stress analyses were performed for transient and steady state conditions. The following boundary conditions were imposed:
l
]'".
The stratification thermal loading was applied as follows:
I ju The results of the stress analyses are provided in the Tables 3-1 and 3-2. The stratification loading stress plots are included in Attachment B.
Table 3-1: Results of Profile 1 Loading (stresses in ksi)
Time Max Stress Stress Radial Stress Hoop Axial Temp at (seconds)
Intensity Intensity at Stress at Stress at Node 99 (Node) at Node 99 Node 99 Node 99 Node 99
(*F)
[
3.u Notes to Table 3-1:
- 1) Node 99 is at the top outer surface of the valve weld. Nodes 1134,776 and 778 are on the pipe inner surface. Nodes 1137,645 and 644 are on the valve inner surface.
- 2) Radial stress is Sxx, hoop stress is Syy and axial stress is Szz at node 99.
Attachment to MSE-SMT-96-031 8
l Table 3-2: Results of Profile 4 Loading (stresses in ksi)
Time Max Stress Stress Radial Stress Hoop Axial Temp at (seconds)
Intensity Intensity at Stress at Stress r.t Node 99 in Model at Node 99 Node 99 Node 99 Node 99
(*F)
I i
}ax,e As shown for the two loadings analyzed, [
j e.e,
1 4.0 TEMPERATURE MONITORING CRITERIA DEVELOPMENT Temperature monitoring criteria was developed based upon fatigue usage at the isolation valve inlet weld, which was judged to be the critical component for thermal stratification effects. The design fatigue usage [
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Attachment to MSE-SMT-96-031 9
4.1 Peak Stress Intensity Range The Reference 12 piping design specification identifies the 1977 edition of the ASME Code through the Summer 1979 addendum (Reference 13) to be the applicable for fatigue analysis.
The peak stress intensity range (S ) between every pair of load sets must be determined to p
calculate the alternating stress intensity (S ), and subsequently the fatigue usage. The a
maximum stress intensity [
- jaxe, l
)
]#.
4.2 Alternating Stress Intensity and Allowable Cycles The alternating stress intensity for a load set is calculated as one-half of the peak stress intensity range multiplied by the factor K,:
i K,
1.0, for S, less than or equal to 3S,
=
1.0 + [(1 - n)/n(m - 1)](S,/3S, - 1),
=
j for 3S, < S, < 3mS, 1/n, for S, greater than or equal to 3mS,
=
where S, primary plus secondary stress intensity
=
S.
allowable design stress intensity
=
0.3 (material parameter from Reference 13) n
=
1.7 (material parameter from Reference 13) m
=
i S, is 16.88 ksi for SA376 Gr 316 stainless steel at 620 F (highest potential temperature at the valve weld based on RCS temperature, and conservative for K, calculation), therefore K,
1.0, for S, less than or equal to 50.64 ksi
=
-2.333 + 0.0665,, for 50.64 ksi < S, < 86.09 ksi
=
3.333, for S, greater than or equal to 86.09 ksi
=
Attachment to MSE-SMT-96-031 10
The primary plus secondary stress intensity [
l l
]"' are provided in Table 4-2.
Table 4-1: Weld and Pipe Stresses (ksi) for Fixed and Free End Conditions i
Radial Hoop Axial Shear Shear Shear Stress Stress Stress Stress Stress Stress Node Sxx Syy Szz Sxz Sxy Syz S1 S2 S3 Sint
[
jo, Notes:
- 1) Nodes 25 and 99 are the weld inside and outside surface nodes, respectively.
- 2) Nodes 121 and 161 are the pipe inside and outside surface nodes, respectively.
- 3) Si, S2 and S3 are principal stresses.
- 4) Sint is stress intensity.
Attachment to MSE-SMT-96-031 11
Table 4-2: Determination of Primary Plus Secondary Stress Intensity for Ke Calculation Radial lloop Axial Shear Shear Shear Stress Stress Stress Stress Stress Stress Node Sxx Syy Szz Sxz Sxy Syz S1 S2 S3 Sint
[
)..ce As shown in Table 4-2, the maximum primary plus secondary stress intensity occurs at the [
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ja.ce, The peak stress intensity range was determined to be [
i
- jaee, For stratification cycles combined with [
)..ce, Values from the fatigue curve for various AT values are provided in Tables 4-3 and 4-4.
Attachment to MSE-SMT-96-031 12
Table 4 3: Allowable Cycles for Stratification Cycles Combined with Themselves AT (Difference in S.
S, So, Allowable Stratification Delta (ksi)
K, (ksi)
(ksi)
Cycles Temperature), "F
[
1
)
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Attachment to MSE-SMT-96-031 13
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Table 4-4: Allowable Cycles for Stratification Cycles Combined with the Zero Load Case AT (Difference in S,
S, S,
Allowable Stratification Delta (ksi)
K, (ksi)
(ksi)
Cycles Temperature), 'F I
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Monitoring Criteria The allowable number of cycles shown in the tables above are for only one stratification delta temperature difference. In reality, stratification will occur at many temperature levels, therefore, the monitoring criteria must include several temperature " bins" to account for this.
[
]"#. Therefore, the temperature monitoring criteria which are established ensure that the ASME Code fatigue limits are not exceeded.
Table 4-5: Residual Heat Removal Temperature Monitoring Criteria Stratification Allowable Cycles from Delta S-N Curve Temperature Allowable Incremental Differential Strat.-
Strat.-
Monitoring Fatigue Range (*F)
Strat.
Zero Cycles Usage l
3us So long as the temperature monitoring distribution is less than or equal to the values shown in the table above, the residual heat removal lines will be within the bounds of the ASME fatigue limits. Note that a lower stratification delta temperature differential may be accounted for by a higher temperature range, if the lower temperature range is maximized. For example, [
]"#. Alternatively, fatigue usage may be tracked either manually, or be an automated system, using the allowable cycles from the fatigue curve.
Cycles are counted in a manner consistent with the thermal event monitoring system (Reference 14) which is currently in use at V. C. Summer. This method sequentially pairs the highest and lowest stratification differential temperatures to determine cycles of stratification AT differential temperatures.
I l
Attachment to MSE-SMT-96-031 15 i
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5.0
SUMMARY
AND CONCLUSIONS P 'he request of SCE&G, Westinghouse has reviewed monitoring data from the V. C.
wununer residoni heat removal piping, and has developed temperature monitoring data 4
acceptance criteria for the RHR lines, based on finite element thermal and stress analysis.
Residual heat removal monitoring data from 1993 through 1995 indicates that temperatures for the Loop C residual heat removal line are exceeding the current acceptance criteria of 50 F. The top to bottom of pipe temperature differential is approximately 160 F (about 360 F at the top of the pipe and 200 F at the bottom of the pipe) and has been relatively steady for about one year. The Loop A residual heat removal line temperature is approximately 100 F at the top of the pipe, with no significant fluctuations. The temperature at the bottom of the pipe is unavailable, but is assumed to be approximately the same as the temperature at the top of the pipe, since it should not be higher than the top temperature.
The Loop A and Loop C layouts are essentially the same with respect to turbulent penetration heating, and one would expect similar temperatures in the horizontal piping near isolation valves 1-8702A and 1-8702B. However, as noted above, there are significant differences in the temperature distribution of the two lines. The reason for the difference [
]'##.
A finite element model of the pipe and isolation valve weld region was created and analyzed for thermal stratification effects. Both transient and steady state thermal and stress analyses were performed. [
]'*".
Subsequent calculation of alternating stress intensity was used to develop monitoring criteria, which is provided in Table 4-5. This acceptance criteria is applicable to both the Loop A and Loop C residual heat removal lines, and is defined in terms suitable for automated surveillance.
Stratification is currently being experienced in the Loop C RHR line, with a top to bottom of pipe temperature differential of 160 F. Monitoring data from this line indicates that stratification remains relatively constant throughout plant operation, with stratification cycles only occurring as a result of plant heatup and cooldown. For this condition, one cycle is defined as a temperature excursion to the stratified condition during normal plant operation and returning to ambient temperature during plant cooldown. As there have been only a limited number of plant heatup/cooldown cycles at V. C. Summer (about 30 per SCE&G),
and the allowable number of monitoring cycles from Table 4-5 is [
]'"#, it is concluded that the observed stratification is well within the acceptable monitoring criteria limits. It also represents a sufficient margin to accomodate this stratified condition for the life of the plant.
To approximate the fatigue cumulative usage factor (CUF) for the current stratified condition, Table 4-4 may be used. From this table, the allowable cycles [
]
Based on 30 cycles accumlated to date, the CUF is [
]'*" 0.0054. Assuming 200 plant heatups and cooldowns for the design life of the plant, the CUF is [
]'*# 0.036.
Attachment to MSE-SMT-96-031 16
6.0 REFERENCES
1)
United States Nuclear Regulatory Commission Bulletin 88-08, " Thermal Stresses m Piping Connected to Reactor Coolant Systems," June 22,1988; Supplement 1, June 24, 1988; Supplement 2, August 4,1988 and Supplement 3, April 11,1989.
2)
Westinghouse Report WCAP-11979, "A Program for Inservice Inspection and Monitoring to Mitigate Concerns for Abnormal Thermal Cycling in Unisolable Piping Segments Connected to the Reactor Coolant System of the Virgil C. Summer Nuclear Power Plant," September 1988, Westinghouse Proprietary Class 2.
3)
Westinghouse Report MT-SME-071, " South Carolina Electric and Gas Company Virgil C. Summer Nuclear Station Unit 1 Identification of Unisolable Piping and Determination of Inspection Locations per NRC Bulletin 88-08, Supplement 3,"
February 1990, Westinghouse Proprietary Class 2.
4)
SCE&G Telecopy from C. Barbier to P. Strauch,05/26/95.
5)
SCE&G inter-office correspondence CGSS-95-0677, 07/13/95, " Virgil C. Summer Nuclear Station ECCS Temperature Monitoring Data NRC Bulletin 88-08," which contains Engineers Technical Work Record Serial No.15053, C. Barbier,07/13/95,
" Review-IEB88-08 Temperature Data."
6)
SCE&G Letter No. CGSW-95-0035, "IEB 88-08, ECCS Temperature Monitoring, RHR Data Evaluation / Acceptance Criteria," 07/13/95 (Work Authorization Form).
7)
Electric Power Research Institute Report EPRI TR-103581, Project 3153-02, entitled
" Thermal Stratification, Cycling, and Striping (TASCS)," March 1994, prepared by Westinghouse Electric Corporation, EPRI Proprietary Licensed Material.
8)
Gilbert Associates, Inc. drawings C-314-641, Sheet 1, Rev. 6, and Sheet 2, Rev. 7 9)
Diamond Power drawings IMS-26-027, Sheet 1, Rev. 4, and Sheet 3, Rev. 4.
10)
Westinghouse EMD drawing 1164E89, Sheet 1. Rev. 5, Motor Operated Gate Valve, Model 12000GM88SEH01,12-1500 ASME Class 1, GPO Assembly.
I1)
WECAN/PLUS, Version Release 90-2 (20402403020), Westinghouse Proprietary, letter MSE-RAEA-297,11/09/94, "WECAN 94 Release Letter", A. Kuenzel.
Verification effort is documented in CN-STD-94-167-RO.
12)
Virgil C. Summer Nuclear Power Plant Piping Design Specification 955136, Revision 1, 07/30/93.
13)
ASME Boiler and Pressure Vessel Code,Section III,1977 edition through Summer 1979 addendum.
14)
Westinghouse Report WCAP-14437, "WES-TEMS Functional Specification for V. C.
Summer Nuclear Station," December 1995, Westinghouse Proprietary Class 2C.
Attachment to MSE-SMT-96-031 17
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ATTACHMENT A Temperature Plots from Program WECAN/Plus 4
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