ML17139A927
| ML17139A927 | |
| Person / Time | |
|---|---|
| Site: | Susquehanna  |
| Issue date: | 08/31/1982 |
| From: | Teske M, Jason West, Williamson G ANDERSON-GREENWOOD & CO., CONTINUUM DYNAMICS, INC. |
| To: | |
| Shared Package | |
| ML17139A925 | List: |
| References | |
| 82-4, 82-4-R, 82-4-R00, NUDOCS 8208170257 | |
| Download: ML17139A927 (82) | |
Text
C.D. I. REPORT NO. 82-4 MARK II PRIMARY CONTAINMENT VACUUM RELIEF VALVE TEST PROGRAM PHASE IV Revision 0 Prepared by Guy G. Williamson Milton E. Teske Alan J. Bilanin CONTINUUM DYNAMICS, INC.
P.O. BOX 3073 PRINCETON, NEW JERSEY 08540 J. Alan West ANDERSON, GREENWOOD 5 COMPANY P.O. BOX 1097 BELLAIRE, TEXAS 77401 Prepared for BECHTEL POWER CORPORATION P.O. BOX 3965 SAN FRANCISCO, CALIFORNIA 94119 Under Technical Services Agreement No. 8031-M-169 AUGUST, 1982 8208170257 8208i3 PDR ADOCK 05000387 c P PDR . . iI
TABLE OF CONTENTS Section ~Pa e INTRODUCT ION 1.1 Background 1.1 1.2 Program Objectives 1.1 1.3 Test Program Summary and Conclusions 1.1 1.4 Description of Report Sections 1.4 SINGLE BAR LINKAGE DESIGN 2.1 SELECTION OF TEST CONDITIONS 3.1 3.1 Selection of Pool Swell Pressure Time Histories 3.1 3.2 Vacuum Breaker Valve Dynamic Response to Pool 3.1 Swell Time Histories 3.3 Predicted Response of Anderson, Greenwood 5 Co. 3.1 24" Vacuum Breaker Valves to Selected Pool Swell Time Histories TEST RESULTS 4.1 4.1 Test Matrix 4.1 4.2 Opening Impact Test Results ; Valve Disc Angular 4.3 Displacement and Angular Velocity 4.3 Closing Impact test Results - Valve Disc Angular 4.3 Displacement and Angular Velocity 4.4 Summary of Strain Gage Data 4.8 4.5 Functional Test Results 4.8 4.5. 1 Leakage 4.8 4.5. 2 Vi sua1 4. 11 4.5.3 Static Torque Tests 4. 15 4.6 Test Chronology 4. 22 4.7 Summary of Test Results and Conclusions 4. 25 TEST FACILITY AND OPERATION 5.1 5.1 General Description 5.1 5.2 Opening Test 5.1 5.3 Closing Test 5.1 5.4 Torque Test 5.1 5.5 Leak Test 5.1 5.6 Sample Test Procedures 5.2 6 TEST VALVE 6.1 6.1 General Description 6.1 6.2 Limerick/Susquehanna Test Valve 6.1 6.3 Shoreham Test Valve 6.1
TABLE OF CONTENTS (CONT'D)
Section ~Pa e INSTRUMENTATION REQUIREMENTS 7.1 7.1 Measurements Required 7.1 7.2 Instrumentation Characteristics 7.1 7.3 Sensor Locations 7.1 QUALITY ASSURANCE
8.1 REFERENCES
9.1 APPENDIX A A.1
ILLUSTRATIONS
~Fi ure ~Pa e 2.1 Theoretical static main shaft torque versus valve 2.2 disc angle.
3.1 Hydrodynamic torque measured data and analytic fit 3.2 3.2 Predicted versus measured nominal impact velocities 3.3 4.1 Test No. 4L4 4.4 4.2 Test No. 4S4-1 4.5 4.3 Test No. 4L5-1 4.6 4.4 Test No. 4L5-2 4.7 4.5 Test No. 4X93 4 9 4.6 Bearing drawing 4.14 4.7 Test No. 4L1-4 torque versus 8 4. 16 4.8 Test No. 4L1-8 torque versus 0 4. 17 4.9 Test No. 4S1-1 torque versus 6 4. 18
- 4. 11 Test No. 4X94 torque versus 6 4. 20
- 4. 12 Test Nos. 4L1-4 and 4X94 strain No. 8 versus 6 4. 21 5.1 Impact test fixture 24" CV1-L 5.3 5.2 Pneumatic system 5.4 5.3 Leak testing schematic 5.5 5.4 Torque versus 6 test procedure 5.6 5.5 Visual inspection and operability checklist 5.7 5.6 Test procedure for phase IV tests 5.8 6.1 24" Vacuum br'eaker valve (front) 6.2 6.2 24" Vacuum breaker valve (back) 6.3 6.3 Shoreham spring cylinder rework 6.6 7.1 AGCo vacuum breaker: phase IV test program instrumentation 7.3 schematic 7.2 Strain gage locations (Limerick valve): gages Nos. 1-4 7.6 7.3 Strain gage locations (Limerick valve): gages Nos. 5-7 7.7 7.4 Strain gage locations (Limerick valve): gages Nos. 8-10, 13 7.8 7.5 Strain gage locations on main shaft: gages Nos. 9A, 9B, 11A, 7.9 11B, 12A and 12B 8.1 Test performance flow diagram 8.2
1 INTRODUCTION
- 1. 1 Background The testing documented in this report is part of an ongoing effort to upgrade the capability of the Anderson, Greenwood & Co. 24 in. vacuum breaker valve to withstand opening and closing impact loads due to predicted pool tivee pressure transients.
swell Earlier phases of the test program identified those components of the present valve design which, when altered, would upgrade the capability of the valves to withstand higher impact loads'hase IV of this program is the testing of the valve using the redesigned components representa-of the valves installed at the Susquehanna power plant. The next scheduled phase of this program is to test the valve with all of its modifications in pl ace.
1.2 Program Objectives The primary purpose of the Phase IV test program is to demonstrate that the vacuum breakers with higher strength critical parts can sustain opening and closing actuations at the impact velocities which are anticipated during pool swell. The test impact velocities are those which would obtain with the pro-posed single bar linkage configuration and 0.5 psi set pressure at Limerick and Susquehanna, as well as the proposed single bar linkage and 0.25 psi set p ressure at Shoreham.
1.3 Test Program Summary and Conclusions A series of opening and closing impact tests were run with angular velo-cities chosen to match those values predicted for the Susquehanna, Limerick and Shoreham configurations during pool swell. No visible or measurable valve damage occurred, nor was the valve functionality impaired in the Susquehanna/Limerick test series. Some deformation of the ring flange was observid after the highest velocity opening impact test in the Shoreham configuration test series. While this damage did increase the leak rate through the valve, it was still well within acceptable limits. Based on the test data taken, the valve was judged to operate satisfactorily after the highest opening and closing impact velocities predicted to occur in a pool swell event in the Susquehanna, Limerick or Shoreham plants.
1.4 Description of Report Sections The remainder of the Phase IV documentation is divided up as follows:
Section 2 - presents the rationale for the change in the spring cylinder to main shaft linkage system from four bars to a single bar.
Section 3 - reviews the simulation of the valve response to pool swell leading up to the specification of nominal impact velocities for the Phase IV test program.
1.1
I Section 4 - presents the results of the test program.
Section 5 - describes the special fixture constructed for the static torque and impact tests, the auxiliary equipment for the leakage tests, and the test procedures employed.
Section 6 - describes the test valve in general, and the modifications to the valve tested in Phase IV.
Section 7 - lists the sensors used, their locations, associated signal conditioning components and the'ata acquisition system.
Section 8 - describes the quality assurance program adhered to in testing.
1.2
2 SINGLE BAR LINKAGE DESIGN Initial fabrication of the Anderson, Greenwood & Co. 24 in. vacuum breaker check valve had the spring cylinder connected to the pivot (main) shaft by a four bar linkage designed to produce a decrease in torque with an increase in the opening angle of the valve disc (Fig. 2.1). This design allows the valve to open quickly to full capacity and to quickly relieve mild pressure transients. However, this statically unstable relationship between torque and valve disc angle results in very high opening impact velocities when the valve is subjected to the largest pressure transients anticipated in a pool swell event.
Simulations have shown that the maximum opening impact velocity for such events can be reduced if the restoring torque on the main shaft, produced by the spring cylinder, increases with the increasing valve disc opening angle. Such a relation can be obtained (Fig. 2. 1) using a single bar to link the main shaft to the spring cylinder. This connecting linkage has been retrofitted at Pennsylvania Power 8 Light (PP8L) and is the linkage configuration studied in Phase IV of this test program.
2.1
Static Main Shaft Torque vs Valve Disc Angle 4000 Single Bar Linkage t
3000 O
l Four Bar Linkage 2000 IOOO CO 0.2 0.6 0.8 I.O l.2 Valve Disk Angle (Rad)
Figure 2.1 Theoretical static main shaft torque versus valve disc angle 2.2
3 SELECTION OF TEST CONDITIONS 3.1 Selection of Pool Swell Pressure Time Histories Pool swell pressure transients used in this analysis have been taken from prior experimental studies by General Electric Co. and adjusted to reach specific peak pressures or to compensate for different pool tempera-tures. These pressure transient driving functions are described in Ref. 1.
3.2 Vacuum Breaker Valve Dynamic Response to Pool Swell Time Histories Prediction of the vacuum breaker valve dynamic response to the pressures developed in a pool swell event are calculated using a valve model/computer code which is documented in Ref. l. Estimates of the hydrodynamic torque developed by the valve disc as a function of valve disc angle are based on values measured at the Anderson, Greenwood 8 Co.- flow test facilities at El Campo, Texas. The test data and the analytic function fit to them are shown in Fig. 3. 1. The predictions of valve disc velocity based on the C.D. I.
valve dynamics code (Ref. 2) using the hydrodynamic torque curve shown in Fig. 3. 1 are conservative when compared with the test data taken in Phase II of this program. This comparison is shown in Fig. 3.2.
3.3 Predicted Response of Anderson, Greenwood 8 Co. 24 in. Vacuum Breaker Valves to Selected Pool Swell Time Histories The C.D. I. vacuum breaker code was run with geometric, mass and spring cylinder torque characteristics representative of the Anderson, Greenwood valves configured for Limerick/Susquehanna and for Shoreham (Table 3. 1) for the six pool swell pressure time histories discussed in Section 3. 1. The responses with the highest opening and closing velocities for each valve configuration where selected for determining the desired experimental test conditions.
The primary experimental test condition to be achieved in the opening impact tests is the predicted angular velocity at impact. A secondary require-ment is that the tension in the cable pulling the disc open be reduced near impact since a large concentrated load at the center of the disc would not be present in a real event.
Choosing appropriate experimental test conditions for the closing impact tests is complicated by the difficulties in estimating the angular velocity of the valve disc near closing impact (e<15') and in relating it to the predicted disc motion in this region. First, the flexibility of the arm and the loose fit of the key mating the arm to the main shaft are significant sources of inaccuracy in estimating instantaneous disc angular velocity based on the measurement of the main shaft angular velocity. Second, the disc is not perfectly parallel to the seat at the time of impact, thus spreading the event out over a significant time interval. Third, Phase II test data showed rapid deceleration of the main shaft just prior to closing impacts due to friction 3.1
I.25 x
X X X
Xx X Xy I.O X x
a O
0.75 XX 0.5 0.25 0.0 lO 20 50 40 50 8 {Deg)
Figure 3.1 Hydrodynamic torque measured data and analytic fit 3.2
12
~ ~
Me...,ed
'"'"'20
-16 -12 -8 12 16 20 predicted (Rad/Sec)
-12 Figure 3.2 Predicted versus measured nominal impact velocities
TABLE 3.1 VALVE GEOMETRIC MASS, SPRING CHARACTERISTICS Parameter Parameter Name Value System moment of inertia 8.1400 lb/in/sec System weight 17.3200 lb System moment arm 10.2900 in System angle from rest* -0.1920 rad Seat angle* 0.0 rad Body angle* 1.30 rad Disc pallet radius 10.26 in Seat coefficient restitution 0.1 Body coefficient restitution 0.1 Spring constant 50 lb/in Limerick/Susquehanna spring preloaded to give 0.5 psi set pressure Shoreham spring preloaded to give 0.25 psi set pressure
- all angles are measured counterclockwise from vertical down.
3.4
in the spring cylinder, four bar linkage and main shaft bearings. These frictional effects are not in the valve dynamic model. For these reasons, it was decided to match the model and experimental valve disc angular velocities at an angle prior to impact where spring cylinder, linkage and main bearing friction were observed to be negligible rather than at impact where the actual system is more complicated than the present valve model.
The desired values of the disc angular velocities to be achieved in the Phase IY experimental test program (nominal impact velocities) are listed below in Table 3.2.
3.5
TABLE 3.2 PHASE IV DESIRED EXPERIMENTAL TEST VELOCITIES PEAK ADJUSTED DESIRED IMPACT POOL SWELL TEST VELOCITY VALVE TEST TYPE LOAD* RAD/SEC Limeri ck/Susquehanna open 15 16 Limeri ck/Susquehanna close -15 Shoreham open 15 19 Shoreham close 15 -14
- (See Ref. 1) 3.6
4 TEST RESULTS 4.1 Test Matrix During the period, May 25, 1982 to July 2, 1982, tests were conducted on Anderson, Greenwood 5 Co. 24 in. vacuum breaker check valves with an assortment of real and simulated, instrumented and uninstrumented components. The main objective of these tests was to evaluate the operability of the valve (leakage'nd flow capacity) after undergoing simulated pool swell events. Secondary objectives were to:
a) Calibrate an air/spring cylinder-actuated test rig to simulate the pool swell events.
b) Measure the static torque produced at the pivot or main shaft by the spring cylinder connected to it by a newly designed single link.
c) Measure the effect of air damping in the spring cylinder to validate this portion of the valve model.
d) Measure the hydrodynamic steady state torque on the main shaft produced by flow generating a measured differential, pressure across the valve disc.
This report documents those tests relevant to the main objective of valve operability appraisal. Those tests relating to the secondary objectives are contained in the Phase IV design record file or the Phase II report (Ref. 3).
The matrix of tests relevent to the main objective is listed in Table 4.1 along with the desired and achieved nominal impact velocities. A more detailed description of these tests and their results follows in the remaining subsections after a brief description of the test numbering system.
Each test is assigned a number made up of four elements as follows:
TEST NO. ($ ) (Y) (K) - (N) where g = phase of test program (4 for all tests discussed in this report)
Y = utility owning the valve configuration being tested L = Limerick/Susquehanna S = Shoreham W = Washington Public Power Supply Systems X = .experimental test non-utility specific (no test type designation)
K = type of test 1 = static torque test 2 = low velocity opening impact test 3 = low velocity closing impact test 4 = nominal opening impact test 5 = nominal closing impact test N = sequence number of test gYK-(i.e. the number of times it has been run).
4.1
TABLE 4.1 PHASE IV TEST t@TRIX Nominal Impact Impact Ini ti al Veloci ty Vel oci ty Angle Desired Achieved Test No. ~Test T e ~de . ~rad/sec ~rad/sec) 4L1-2 Static torque 4Ll-3 Static torque 4L1-4 Static torque 4L2-1 Opening impact, low velocity 4L1-5 Static tor ue 4L4-1 Opening impact 16 4L1-6 Static torque 4L5-1 Closing impact 48 -15 -13 4L1-7 Static torque 4L5-2 Closing impact (spring assisted) 55 -16 4Ll-8 Static torque 4S1-1 Static torque 4S1-2 Static torque 4S4-1 Opening impact 18 4S1-3 Static torque 4X92 Static torque 4X93 Closing impact (spring assisted +2 plus reduced air damping) 60 -2O-O -20 4X94 Static torque 4.2
4.2 Opening Impact Test Results - Valve Disc Angular Displacement and Angular Velocity For the opening impact tests, the valve disc was opened rapidly from the closed to the open position by means of. the air actuator. The cable and actuator were adjusted so'hat the piston of the actuator would bottom out in the cylinder just before the actual impact of the test valve idler arm with the external stop.
The angular position and velocity of the disc are measured by independent sensors located on the end of the main or pivot shaft opposite the spring cylinder. This location was selected since there are no significant strains between the vertical arm/disc assembly and the end of the main shaft other than at the bearing (which has minimal normal forces). Figs. 4.1 and 4.2 show the time histories of the valve disc angle and angular velocity for test 4L4-1 and 4S4-1 respectively. The initial decrease in angular velocity is the result of the reduction in cable tension and the corresponding response of the main shaft. The subsequent extreme decrease in angular 'velocity is the result of the actual impact of the idler arm on the external stop and the disc contacting the. inside diameter (ID) of the valve body as substantiated by rapid changes in all strain gage responses. Note: the angular displacement traces show that the angular momentum of the valve disc causes it to overshoot its maximum static position during the period of rapid deceleration. Velocities at opening impact are 16 and 18 rad/sec respectively for these two tests.
4.3 Closing Impact Test Results - Valve Disc Angular Displacement and Angular Vel oci ty For the closing impact tests, the valve disc was held open at a preselected angle by the air actuator and then released by manually actuating the quick release latch mechanism. The torque from the spring cylinder caused the disc to accelerate to the desired test velocity and then impact the valve seat.
To achieve higher impact velocities additional spring loads were applied by means of industrial type door springs. These springs were attached at the center of the disc with a long cable adjusted to have,no significant load at the time of impact.
The closing impact tests as discussed in Section 3.3 are based on conditions prior to impact (8 = 20o). These conditions have been evaluated based on the value of main shaft velocity averaged over the oscillatory response of the main shaft/disc assembly's torsional mode of response, shown in Fig. 4.3. The displacement time history can be differentiated to provide an independent measurement of the nominal angular velocity at impact.
The nominal angular impact velocity in test 4L5-1 was lower than required by the Test Specification. The test was, therefore, repeated with the valve disc initial angle of opening increased to 55 and two springs attached by cable to the disc center to help pull it closed. In this test, the average angular velocity of the disc at an angle of 20 is 16 rad/sec (Fig. 4.4) which is within the range of acceptable test velocities.
Since the set pressure requi rements dictate a smaller torque versus valve disc angle for the Shoreham configured valve than for the Limerick/Susquehanna 4.3
l5 TEST NO. 4L4-1 OPENING IMPACT Limerick/Susquehanna spring cyl inder 70 Io 50 0
5 30 20 IO IO l5 20
,4 Figure 4.1 Test No. 4L4-1
TEST NO. 4S4-I l5 OPENING II1PACT Shoreham spring cylinder IO 60 50 4p 20 IO IO l5 20 Figure 4.2 Test No. 4S4-1
20 8 TEST NO. 4L5-1 CLOSING IMPACT l5 e 70 Limerick/Susquehanna spring cylinder e(0) = 48 Deg.
lP 60 50 40 30 20 lp 0
20 Figure 4.3 Test No. 4L5-I
8 20 TEST NO. 4L5-2 CLOSING NPACT Limerick/Susquehanna spring cylinder l5 e(o) = 55 oeg.
Oval spring assist e
20 F'igure 4.4 'Test No. 4L5-2
valve (Table 3.1), the anticipated nominal closing impact velocities are lower
~ ~ ~ ~
~
(Table 3.2) as well; therefore, no apparent justification exists for running
~ ~ ~
an additional test at a lower velocity than already investigated.
~ ~ ~
~
Since the test components were still functional, though no longer designated for operational use, and since all test equipment was still in place, additional tests were executed to investigate valve operability at a higher closing velocity than predicted for pool swell. These tests would either identify failure modes of the valve or show that it could sustain higher than necessary nominal closing impacts. Valve operability was still acceptable after the highest nominal closing impact test (Fig 4.5, -20 rad/sec).
4.4 Summary of Strain Gage Data Continuous recordings of all pertinent strain gage outputs (instrumentation schematic Fig. 7. 1) were made during all of the tests listed in Table 4.1. The maximum values attained during each test are the most important data (Table 4.2).
ASME static yield limits were surpassed on the disc and arm in several tests with no permanent deformation. This is due to two factors: (1) the measured yield in the 316SS material is in excess of 1500 pin/in (190 percent of ASME yield) and the* maximum strain exceeded measured yield by only 15 percent and (2) the impulsive application and relief of the applied impact load does not allow enough time for the material to permanently deform.
4.5 Functional Test Results 4.5.1 Leakage-a) Limerick/Susquehanna Test Series Leakage was measured, as described in Section 5, before Test 4L4-1 and after Test 4L5-2. High (30 psi) and low (1 psi) test pressures were checked as required by the Susquehanna Vacuum Breaker Specification. Pre-test results indicated a small amount of leakage (12.5 cc/min) at the lower pressure and zero leakage at the higher pressure. Post-test results indicated zero leakage at both pressures. The allowable leak rate specified for Susquehanna is 100 cc/hr/in or 34.37 cc/min. Visual inspection of the sealing surfaces confirmed that the impacts 'did no damage that would compromise valve sealabi lity.
b) Shoreham Test Series Since there were no changes in the sealing components and the post-test results from the Limerick/Susquehanna test series indicated no leakage, pre-test leakage inspection was not performed for Shoreham. Post-test results showed some degradation of sealability.
A leakage rate of 1220 cc/min was measured at 4 psi (Shoreham Speci-fication test pressure). Although the leakage was signifi cant, it fell well under the allowable leak rate of 1 SCFM or 28317 cc/min specified for Shoreham. Visual inspection indicated that the increased rate of leakage was probably due to local bending of the disc ring flange at the point of contact with the valve body ID.
4.8
TEST NO. 4X93 l5 CLOSING IMPACT 8 Lime ri ck/Susquehanna spring cyl inder 70 with both upper and lower air ports open l0 0(0) = 60 Deg.
60 50 40 20 IO l5 20 Figure 4.5 Test No. 4X93
TABLE 4.2 MAXIMUM STRAINS IN PHASE IV TESTS Susquehanna Material on which Susquehanna Shoreham and Shoreham strain gage Opening Impact Opening Impact Closing Impact is mounted Test Test Test 16 rps 18 rps -16 rps Strain Gages on Main Shaft
¹11 17-4PH -2180 -2260 -1760
¹ 9 2180 2540 -1220
¹12 1220 1840 680 Strain Gages on Arm and Disc
¹8 316SS -1730 -1720 690
¹5 1600 1490 1050
¹2 -250 -110 -950
¹3 700 120 350 Strain Gages on Single Bar Linkage
¹10 316SS 400 380 -420
¹13 -210 -290 -190 Note: ASME static yield values are 805 and 3860 for 316SS and 174PH respect-ively. Measure yield for 316SS components was obove 1500.
- 4. 10
The flatness of the sealing lip was measured to be within .010 in prior to all testing and .033 in following the Shoreham test series.
The seal material showed no signs of degradation due to the impacts.
c) Auxiliary Test Series Post test results showed a further increase in the rate of leakage. Susquehanna test pressure specifications were used for this series since they bracket the Shoreham test pressure. Leak rates of 4000 cc/min and 3100 cc/min were measured at 30 psi and 1 psi respectively after test 4X93.
4.5.2 Visual a) Limerick/Susquehanna Test Series Sealing surfaces and critical components were visually inspected and checked for fit and function before and after each impact test.
Table 4.3 outlines each checkpoint of the inspection.
The results of the visual inspection indicated that there. was no major damage to the valve from either opening or closing impacts.
The following observations were made:
The 1/16th in . diameter cable used for disc anti-rotation was partially sheared by the sharp edge of the disc assembly back plate. It remained in place, but would not have restrained any disc rotation. Also, damage of this cable allowed the disc to tilt forward slightly and wipe the seal. Although undesirable from the standpoint of seal life longevity, the damage was not detrimental to the func-tioning of the valve.
The disc assembly made contact with the valve body ID on opening impact. The external valve stop is adjusted so that under normal actuating loads the disc does not contact the valve body. However, the inertia of the disc was sufficient to flex the column, arm and shaft an additional few degrees, thus allowing the disc to temporarily make contact. Contact was made at two points on the valve body at approximately 10 and 2 o'lock. Scuff marks on the back edge of the disc and gouge marks on the valve body were the only evidence of this contact.
Following the opening impact there was evidence of additional looseness, or "slop," in the connections between the spring cylinder and the disc. The valve position zero (closed) had shifted approximately 1 and the spring cylinder had retracted approximately . 10 in. Subsequent disassembly and inspection indicated a wollowing out or brinelling of the arm keyway. No evidence of cracking or potential failure in the arm was found. This brinelling was expected since the arm material (316 SST) is the softest in that load train. Comparing pre- and post-test torque curves indicates that this additional looseness had a negligible effect, 4.11
TABLE 4.3 VISUAL INSPECTION & OPERABILITY CHECKLIST
- 1. Check that the valve disc is centered on the seat in the valve orifice plate.
- 2. Check the dome surface for deformation, especially around the weld areas.
- 3. Check the lip on the ring flange for nicks, scratches or other damage that could affect sealability.
- 4. Check the diaphragm seal for scratches, tears or other damage that could affect sealability.
- 5. Check that the disc assembly seats uniformly on the seat with no interference.
- 6. Check that the arm turnbuckle jam nuts are tight.
- 7. Check binding in the shaft bearings and spring cylinder and general operability of the valve. Note: this check is primarily based on data obtained in the static torque tests.
4.12
All other inspections made were satisfactory (Table 4.3).
No evidence of any deformation or cracking of the dome or its welds was found. Pre- and post-test torque curves were com-pared to check for binding in the spring cylinder and to verify full open operation.
b) Shoreham Test Series The same visual inspections performed for the Limerick/
Susquehanna tests were performed before and after the Shoreham test. The antirotation cable that sheared during the Limerick/
Susquehanna test was replaced. All other components were in the Limerick/Susquehanna post-test condition. Observations follow-ing the Shoreham opening impact test (4S4-1) were as follows:
- 1) The anti rotation cable sheared as it had in the Limerick/Susquehanna opening impact test. This did not affect the functioning of the valve.
- 2) The disc again contacted the valve body. This time the impact was severe enough to cause slight local deformation of the ring flange lip. The visible damage was a larger scuff area on the back edge of the ring flange and a small wrinkle in the sealing lip. Dimension-ally, the lip flatness was changed from .010 in. before testing to .0333 in after. Functionally, sealability was affected as described in Section 4. 5.1.b.
- 3) All other inspections made per Table 4.3 were satis-factory.
c) Auxiliary Test The same visual inspections were performed before and after the 20 rad/sec closing impact test (No. 4X93). No evidence of further degradation or damage due to this test was found and the valve operated properly.
d) Post-Test Disassembly and Inspection After all testing was completed, the valve was disassembled and each component visually inspected, with the follwoing observations:
- 1) The keys on the spring cylinder link-to-shaft connec-tion were tight and did not exhibit any loosening. The keys on the disc/arm-to-shaft connection fit loosely. The keyway in the arm showed signs of brinelling or flaring out, allowing the key to rock. (See 4.5.2.a).
- 2) After many cycles the shaft and bearing caps on the spring cylinder side showed initial signs of galling (Fig. 4.6) tlarks were in the 12 to 4 o'lock band looking inboard, indicating that bending in the shaft due to the spring cylinder load caused the metal-to-metal contact. Although there were signs of galling after many cycles, the shaft rotated freely with the spring cylinder disconnected. ( In actual operation the vacuum breaker is called upon to cycle open and closed only once in performing its function with respect to a pool swell transient).
4.13
BEAR ING CAP AREA THAT SHOWED SHAFT SIGNS OF GALLING SPRING VALVE CYL INDE R DISC BRONZE BEARING VALVE BODY Figure 4.6 Bearing drawing
- 3) Both spring cylinders were completely disassembled and inspected. The inspection of the parts showed only what would be expected from normal wear.
- 4) No damage to the disc was noted other than the defor-mation described as significant indications in Section 4.5.2.b.
Profile measurements of the dome taken before and after the testing showed no significant change.
4.5.3 Static Torque Tests The cable actuator system was used for the torque measurement test also.
The test valve disc was slowly opened and closed while continuous measure-ments were made of main shaft torque, strain in the arm and the angular position of the disc. The opening and closing rates were controlled by manual manipulation of the block and bleed valves while the solenoid valve was open.
In the low velocity and low acceleration static torque tests where iner-tial effects can be neglected, the main shaft torque (measured by gages No.
llA 5 No. 11B) is the sum of the torques due to spring compression and friction in the following components: single bar, idler arm, sliding and rotating joints in the spring cylinder. The strain in the vertical arm,'easured by strain gage No. 8, is due to the frictional torque in the main bearings as well as the main shaft torque components listed above. The difference in strain in the vertical arm between the opening and closing portions of each slow actuation (hysteresis in the cycle) is a measure of the friction in the train of moving parts from spring cylinder to valve disc. Not all of these test results are shown since it can be reasonably concluded that no increase in the frictional effects or the spring force-displacement relation between the first and last test indicates no changes in between as well. For this reason, the strain gage No. 11 results of tests 4Ll-4 and 4L1-8 are shown (Figs. 4.7, 4.8) as documentation of no changes in the system with the Limerick/Susquehanna spring cylinder in use and tests 4Sl-1 and 4S1-3 (Figs. 4.9, 4.10) for the comparison when the Shoreham cylinder was employed. In addition, main shaft torque measurements from test No. 4X94 are presented (Fig. 4. 11) for comparison with like data prior to the first test (Fig. 4.7). Comparison of these measurements show no significant change in the operating characteristics of the Limerick/
Susquehanna spring cylinder and the associated single bar linkage.
Similarly, a comparison of the pre- and post-test strains developed in the vertical arm while slowly cycling the valve show the same amount of hysteresis before and after testing and a possible decrease in the average cycle strain after testing (Fig, 4. 12). The combination of these data from strain gage No. 11 and strain gage No. 8 confirm what was concluded in the other operability checks i.e., no change in the torque character-istics of the valve due to the impact tests.
4.15
4000 5000 2000 O
l 1000 0 10 20 30 40 50 60 Angle Displacement (Deg)
Figure 4.7 Test No. 4L1-4 torque versus 8
- 4. 16
0000 2000 O
I-1000 I 0 20 '50 40 50 60 Ang le Displacement (Deg)
Figure 4.8 Test No. 4Ll-8 torque versus 6 4.17
4000 3000 2000 L
O l 000 0 lO 20 50 40 50 60 Angle Displacement (Deg)
Figure 4.9 Test No. 4S1-1 torque versus 8 4.18
4000 3000 2000 L
O
!000 IO 20 30 40 50 60 Angle Displacement (Deg)
Figure 4.10 Test No. 4S1-3 torque versus e 4.19
4000 3000 2000 O
I I 000 0 IO 20 30 40 50 60 Ang le Displacement (Deg)
Figure 4.11 Test No. 4X94 torque versus e 4.20
Pretest (4L1-4) 400.0 opening Post test (4X94) opening 300.0 EO O
U 200.0 Pretest (4Ll-4) closing M
Post test (4X94) closing I 00,0 0 IO 20 50 40 50 60 Angle Displacement (Deg)
Figure 4..12 Cyclic strain in vertical arm, strain gage No. 8 4.21
4.6 Test Chronology During the time period, May 25, 1982 to July 2, 1982, over one hundred tests were conducted on the Anderson, Greenwood 5 Co. 24 in. vacuum breaker valve with an assortment of real and simulated, instrumented and uninstrumented components. Following the preliminary May and June tests, the valve was dis-assembled, inspected and reassembled with parts that had not been used in the earlier testing (the valve disc had been used previously in both Phase I and Phase II testing). The valve then underwent leak testing and visual inspection as reported in Sections 4.3. 1 and 4.3.2 on June 15, 1982. The formal Phase IV tests are described below.
TEST NO. 4Ll-4 DATE June 16, 1982 TIME 13:41 A static torque test of the Limerick/Susquehanna configured vacuum valve with new vertical arm bending caps, main shaft, keys and single barbreaker linking the main shaft to the spring cylinder This test completes the baseline functional tests testing. The measured relationship between main shaft prior to actual impact torque and arm strain are shown as a function of the valve disc angle (Fig. 4.7).
TEST NO. 4L2-1 DATE June 16, 1982 TIME 15:20 A low velocity opening impact test of the Limerick/Susquehanna configured vacuum breaker valve to determine the pressure in the accumulator/driving cylinder system necessary to achieve the desired maximum angular velocity of the disc An accumulator pressure of 150 psi, producing a maximum velocity of 9 rps was used for this test. This data point, along with other calibration data, suggests that an accumulation pressure of 225 psi should result in the desired test velocity of 17 ~
rad/sec.
TEST NO. 4L1-5 DATE June 16, 1982 TIME 18:23 A static torque test of the Limerick/Susquehanna configured vacuum breaker valve to check that test No. 4L2-1 did not change the relationship between main shaft torque arm strain and valve disc angle The test data show that no change occurred.
TEST NO. 4L4-1 DATE June 16, 1982 TIME 19:05 An opening impact test of the Limerick/Susquehanna configured vacuum
+0 breaker valve with a desired impact velocity of 17 'ad/sec The test was run with an accumulator pressure of 225 psi and achieved a nominal impact velocity of 16 rad/sec. Time histories of angular position and angular velocity appear in Fig. 4.1.
4.22
Following this test the valve was visually inspected, as reported in Section 4.3.2, and no damage was observed. In addition, test No. 4L1-6 was performed in order to check valve operability.
TEST NO. 4L1-6 DATE June 16, 1982 TIME 20:40 A Static torque test of the Limerick/Susquehanna configured vacuum breaker valve to evaluate the effect of the previous opening impact test (No. 4L4-1) on the relationship between main shaft torque, arm strain and disc angular position No changes were observed in these relationships.
TEST NO. 4L5-1 DATE June 16, 1982 TIME 21:23 A closing impact test of the Limerick/Susquehanna configured vacuum breaker valve with a desired test velocity of 'ad/sec Based on prior calibration data, the initial disc angle of opening was 48 . This initial disc angle resulted in a maximum angular velocity of only
-13 rad/sec (Fig. 4.3). Since this was less than the desired test velocity, the valve test was repeated with a larger initial angle of opening and with a cable/spring assembly attached to the front of the disc to provide additional closing torque, i.e. to stimulate the effect of a hydrodynamic torque in the backwards direction.
TEST NO. 4L1-7 DATE June 16, 1982 TIME 22:41 A static torque test of the Limerick/Susquehanna configured vacuum breaker valve to evaluate the effect of the previous closing impact test (No. 4L5-1) on the relationships between main shaft torque, arm strain and angular position No changes were observed in these relationships.
TEST NO. 4L5-2 DATE June 16, 1982 TIME 22:59 A closing impact test of the Limerick/Susquehanna configured vacuum breaker valve with a desired test velocity of -15+-'ad/sec Based on the results of the previous closing impact test (No. 4L5-1) and prior spring assisted calibration runs, the initial disc angle of opening was 55 deg. In addi tion, two heavy duty springs were attached to the center of the disc by a cable attached to an eyebolt. The length of the cable was adjusted such that the springs exerted no force on the disc at the time of impact. A test velocity of -16 rad/sec was achieved in this test (Fig. 4.4).
Following this test, the valve underwent the full battery of functionality tests. As reported in Section 4.3.1 and 4.3.2, no visual damage was observed and a decrease in leakage from the baseline test was measured. In addition, the static torque test (No. 4L1-8) was performed and no changes were measured in the relationships between main shaft torque, arm strain and disc angle.
4.23
Since the above operability test and visual inspection showed that all components of the valve were in operational condition, the decision was made to use these components, with the exception of the spring cylinder, for the Shoreham valve tests (the Shoreham valve has a 0.25 psi set pressure as opposed to 0.5 psi set pressure for the Limerick/Susquehanna configuration and, therefore, has a different spring/cylinder barrel configuration which must be used in these tests).
TEST NO. 4S1-1 DATE June 29, 1982 TIME 15:26 A static torque test of the Shoreham configured vacuum breaker valve with the single bar linking the main shaft and Shoreham spring cylinder This test of the main shaft torque and arm strain produced by the spring cylinder as a function of valve disc angular displacement (Fig. 4.9), plus the previous leak test and visual inspection, forms the baseline test package for the Shoreham valve tests.
TEST NO. 4Sl-2 DATE June 30, 1982 TIME 09:52 A static torque test of the Shoreham configured vacuum breaker valve to check that the test rig calibration work using the simulated disc did not change the relationship between main shaft torque, arm strain and valve disc angle In this case, the torque required to cycle the valve increased by approxi-mately 100 in/lbs, indicating a possible slight change in the operation of the H'0 spring cylinder.
TEST NO. 4S4-1 DATE June 30, 1982 TIME 11:24 An opening impact test of the Shoreham configured vacuum breaker valve with a desired impact velocity of 19 ~ rad/sec Based on the results of the test rig calibration work, plus test No. 4Sl-2 and analytic work, an accumulator pressure of 200 psi was selected for this test. An impact velocity of 18 rad/sec was achieved (Fig. 4.2).
This test completed the impact testing for the Shoreham configured vacuum breaker valve.
Following this test, the valve underwent the full battery of functionality tests. As reported in Section 4.3. 1 and 4.3.2, visual damage of the ring flange was observed and the leak rate increased, but was still below the maximum acceptable value specified by Shoreham. In addition, the static torque test (No. 4S1-3) was performed with no changes noted in the relationships between main shaft torque, arm strain and valve disc angle (Fig. 4. 10) and the baseline data.
TEST NO. 4X93 DATE July 2, 1982 TIME 14:30 Since the valve was still functioning properly, the decision was made to perform a closing impact test at the highest velocity attainable. This required I
4.24
using the Limerick/Susquehanna spring cylinder, starting with the valve disc held in the full open position, augmenting the closing torque with the auxiliary springs as done in test No. 4L5-2 and removing the orifice restriction at the bottom of the spring cylinder in order to reduce the damping effect of the trapped air. This procedure resulted in a closing velocity of 20 rad/sec with the maximum strain listed in Table 4.2.
Post-test main shaft torque and arm strain measurements versus disc angle agreed with pre-test values. As reported in Sections 4.5. 1 and 4.5.2, the visual inspection showed no new damage and the leak rates were 4000 cc/min and 3100 cc/min at 30 psi and 1 psi respectively.
4.7 Summary of Test Results and Conclusions A series of opening and closing impact tests was run with angular velocities chosen to match those values predicted for the Susquehanna, Limerick and Shoreham configurations during pool swell. No visible or measurable valve damage occurred, nor was valve functionality impaired in the Susquehanna/Limerick test series.
Some deformation of the ring flange was observed after the highest velocity opening impact test in the Shoreham configuration test series. While this damage did increase the leak rate through the valve, it was still well within acceptable limits. Based on the test data taken, the valve was judged to operate satisfactorily after the highest opening and closing impact velocities predicted to occur in a pool swell event in the Susquehanna, Limerick or Shoreham plants.
An additional closing impact test was run to evaluate valve operability at even higher velocities. The valve was closed at a test velocity of 20 rad/sec.
Visual inspection indicated no increase in valve deformation and the final leak rate measurements were 4000 cc/min and 3100 cc/min at 30 psi and 1 psi respectively.
4.25
e 5 TEST FACILITY AND OPERATION 5.1 General Description A special fixture for performing all impact tests was constructed at the Anderson, Greenwood 8 Co. facilities in Houston, Texas. The fixture provides support for the test valve, cable system and air actuator in a compact and rugged structural unit (Fig 5. 1). Air pressure supplied by an air receiver is used to pull the valve open using the cable/pulley system shown in Fig 5. 1.
A quick opening solenoid valve is used to apply the pressure to the actuator rapidly. The pressure in the air receiver is set to different values to obtain different values of opening impact velocity. The cable system has a three to one velocity amplification so as to keep the maximum actuator rod velocity to less than 50 in/sec. The schematic diagram of the pneumatic system is shown in Fig 5.2.
5.2 Opening Test For the opening impact tests, the valve disc was opened rapidly from the closed to the open position by means of the air actuator. The cable and actuator were a'djusted so that the piston of the actuator would bottom out in the cylinder just before the actual impact of the test valve disc and mechanism.
The quick release device shown in the cable system was not used for this test.
5.3 Closing Test For the closing impact tests, the valve disc was held open with the air actuator to a preselected angle and then released by manually actuating the quick release latch mechanism. The torque from the spring cylinder caused the disc to accelerate to the desired test velocity and then impact the valve seat. To achieve higher impact velocities additional spring loads were applied by means of industrial type door springs. These springs were attached at the center of the disc with a long cable adjusted to have no significant load at the time of impact.
5.4 Torque Test The cable actuator system was used for the torque measurement test also.
The test valve disc was slowly opened and closed while continuous measurements were made of mainshaft torque, strain in the arm and the angular position of the disc. The opening and closing rates were controlled by manual manipulation of the block and bleed valves while the solenoid valve was open.
5.5 Leak Test Seat leakage tests were made before and after impact testing. The test valve outlet port was closed off with a blind flange. Back pressure was applied through a regulated air supply. The test pressure was stabilized at the valve desired with the regulator adjusted so that the flow into the valve 5.1
just equaled that of the leakage out. Repeated readings were then made of the flow into the valve through the rotometer as shown in Fig 5.3. With valve number 1 closed and valves numbers 2 and 3 open, the total flow through the rotometer equaled the leak rate when stabilized conditions were maintained.
5.6 Sample Test Procedures Figs. 5.4 through 5.6 are samples of the test procedures and checklists used in the test program.
5.2
lg Qo 0 ARCLC OF ROTATOH TAIrCK TrFLE'SE 0
0 TWO IfP NPT CONrEC T IOUS FOR AH STrpPLY Oo Oo TFST TlALVE 4'ArR ACTUATOR Figure 5.1 Impact test fixture 24" CV1-L
3/4" NPT 3/4 NPT SOLENOID VALVE SAFETY VALVE SET AT 250 PSIG I NPT BLOCK PRESSURE GAUGE VALVE BLEED VALVE AIR RECEIVER AIR ACTUATOR I/2'LEX HOSE Figure 5.2 Pneumatic system
BLEED VALVE O'I AIR SUPPLY PRESSURE REGULATOR VALVEQ3 TEST VALVE VALVEg2 ROTOM ETER Figure 5.3 Leak testing schematic
TORQUE VS 8 TEST PROCEDURE T-25-ll-Rev. 1 6/15/82 Test Valve Arm Disk Shaft Link Performed Checked by by Cylinder with 50 lb/in Spring RVDT Channel 12 SG-ll Channel 6 PT-12 Channel "1 Turn on Visicorder Channels 6 - 11 12 with gains set at .2; .2; .2 volts/division paper speed set at 0.4 ips time line set at 1 sec.
Turn on Tape Recorder Start footage: Start time:
Stop footage: Stop time:
Cycle va've open and closed times Turn Off Visicorder Date: Time:
Performed by:
Verified by:
Q.A. Verification:
Figure 5.4 Torque versus e test procedure 5.6
VISUAL INSPECTION AND OPERABILITY CHECKLIST ITEMS TEST NO. 1 2 4 5 8 9 10 COMMENTS TEST OBSERVERS
- 1. Disc is centered in orifice plate
- 2. Dome
- 3. Seal lip on ring flange
- 4. Diaphragm seal
- 5. Disc seats uniformly on seal without interference
- 6. Arm jam nuts are tight
- 7. No binding in shaft bearings
- 8. No binding in spring cylinder or mechanism
- 9. No binding in operator cylinder
- 10. Operability check Figure 5.5 Visual procedure and operability checklist
Date Start time TEST PROCEDURE FOR PHASE IV TESTS C.D.I. PROCEDURE T25-08-RV 3(TEST SERIES 1 PRETEST REQUIREMENTS 1.1 TIME CODE GENERATOR/READER The time code generator time wi11 be checked for correct time &10 min. perf. chkd.
- 1. 2 CALIBRATE RECORDING EQUIPMENT 1.3 RECORD ON MAG TAPE FOOTAGE TINE
- l. 4 RECORD ON OSCI1.LOGRAPH 1.5 SET BIAS I.EVELS ON STRAIN GAGE AMPS TO ZERO 1.6 VERIFY SUFFICIENT PAPER IN OSCILLOGRAPH-, MAG TAPE IN DATA RECORDING TAPE RECORDER AND PRO-PER POSITIONING OF TAPE ON INPUT TAPE RECORDER 1.7 VERIFY TAPE RECORDER NOT IN CA1 MODE 2 TEST SEQUENCE 2.1 START TEST DATA TAPE RECORDER (INITIATED BY FOOTAGE TL~AE
- 2. 2 START TEST DATA OSCIL1.0GRAPH 2.3 INITIATE TEST 2.4 SHUT OFF OSCILLOGRAPH 2.5 SHUT OFF TFST DATA RECORDER 2.6 PERFORM VISUAL INSPECTION AND OPERABILITY CHECK (CHECKLIST + T25-ll) 2.7 SET UP FOR NEXT TEST IN SERIES OR GO TO 3.1 3 POST TEST PROCEDURES 3,1 CALIBRATE RECORDING EQUIPMENT 3.2 RECORD ON MAG TAPE FOOTAGE TIME 3.3 RECORD ON OSCILLOGRAPH
- 3. 4 PLAY BACK YAG TAPE DATA ONTO OSCILLOGRAPH TO CHECK TO VALID RECORDING OF DATA IF NOT DONE DURING TEST COMIENTS:
End time Per formed by Chaciced by OA. Vo. i: ed Figure 5.6 Test procedure for Phase IV tests 5.8
0 6 TEST VALVE
- 6. 1 General Description The valve evaluated in this program is Anderson, Greenwood 8 Co.'s 24 in. CVl-L Vacuum Breaker Check Valve (Figs. 6.1 and 6.2), a swing-type check valve using a light weight low inertia disc. The disc is held closed against an elastomeric diaphragm seat by an external spring cylinder. The valve is self-actuated by pressure differentials across the disc. This product was designed and built to the specifications for Primary Containment Vacuum Relief Valves for the following nuclear power plants: Limerick 1 & 2
'PECO); Susquehanna 1 8 2 (PP8L); Shoreham (LILCO).
Although minor differences between the valves do exist, they are primarily in the auxiliary equipment of each valve. The critical components as defined by preliminary analysis are compared in Table 6.1- For the purposes of this test program, Limerick and Susquehanna are considered identical. The Shoreham valve is identical to Limerick and Susquehanna except for its lower specified set pressure. This difference in set pressure only affects the spring cylinder.
6.2 Limerick/Susquehanna Test Valve The valves used in the test program were provided by Philadelphia Electric Co. from the Limerick Generating Station. Assembly drawings for these valves as originally configured are included in Appendix A. One of these valves was modified as follows for testing:
a) Some critical components were replaced with higher strength material as shown in Table 6.2.
b) The four-bar linkage was replaced with a single bar linking the main shaft to the spring cylinder. The modified assembly included an idler link to limit the open position of the valve disc.
c) The key mating the single bar to the main shaft was machined to produce a tight fit between these two components.
d) Threaded bushings were welded to the arm shank in order to attach a connector to the cable system from the test fixture.
Other than the above specified modifications, the Limerick/Susquehanna test valve was identical to that shown in Appendix A.
6.3 Shoreham Test Valve To assure that the Shoreham Test Series was representative of a new valve (i.e., no previous impacts) the test plan called for a completely new set of internal parts to be used. However, since there was no indication of component damage in the Limerick/Susquehanna test series, the test conductor chose to proceed using the same test valve. The only component changed was the spring cylinder. A spare spring cylinder from the Shoreham plant was provided by Long Island Lighting Co. for this test. The standard springs in this cylinder were replaced with higher rate springs (same rate as Limerick/Susquehanna) to develop the desired restoring torque characteristic (Fig. 6.3).
6.1
Figure 6.1 24" VACUUM BREAKER VALVE
.25 TO .50 PSID SET PRESSURE 6.2
d
]
~i
, dg+
A Figure 6.2 24" VACUUM BREAKER VALVE
.25 TO .50 PSID SET PRESSURE 6.3
TABLE 6.1 COMPARISON OF CRITICAL COMPONENTS COMPONENT LIMERICK SUS UEHANNA SHOREHAM Orifice Plate 0 Ring Retainer 0 Arm Assembly 0 Cap, Bearing 0 Disc Assembly X Shaft, Pivot 0 Shaft, Column 0 Spring Return Force X 0 - Means parts are identical.
X - Means parts are not identical.
NOTES The Shoreham di sc i s sl i ghtly thi cker than the Limer i ck/Susquehanna di sc.
2 The Shoreham spring preload (force with valve in closed position) is half the value of the Limerick/Susquehanna spring preload. The spring rates are the same.
6.4
TABLE 6.2 VALVE COMPONENTS WITH HIGHER STRENGTH MATERIAL OLD PART NO. NEW PART NO.
DESCRIPTION MATERIAL MATERIAL KEY 05-1039-004 05-1039-009 316 SST ASTM A564-630 (17-4 PH)
KEY 05-1039-005 05-1039-010 316 SST ASTM A564-630 (17-4 PH)
SHAFT N03-7915-001 N03-7915-002 ASME SA 479-316 ASTM A564-630 (17-4 PH)
TURN BUC KL E 04-3010-001 04-3010-002 ASTM A269-304 ASTM A564-630 (17-4 PH)
COLUMN 03-8180-001 03-8180-004 ASTM A269-304 ASTM A564-630 (17-4 PH) 6.5
- 1) Cut rod to length specified
- 2) Replace springs (2) with new springs (04-3078-006)
I"1 Fi gure 6. 3 Shoreham spring cyl inder rework 6.6
7 INSTRUMENTATION REQUIREMENTS
- 7. 1 Measurements Required The following variables were measured in order to demonstrate vacuum breaker operability't the maximum impact velocities anticipated during pool swell:
a) Angular position of the valve disc b) Angular velocity of the valve disc c) Strain at selected locations and areas on the critical components d) Differential air pressure across the air spring cylinder piston or across the piston of the air operator when these devices are used to provide increased damping e) Pre-test and post-test valve leakage.
7.2 Instrumentation Characteristics Table 7. 1 summarizes the measurement requirements with regard to range, accuracy and frequency bandwidth. The flow of data from the sensors, through the signal conditioning components and into the data acquisition system is shown in Fig. 7.1.
7.3 Sensor Locations Angular Displacement A Schaevitz Model R30D rotary variable differential transformer (RVDT) is attached to the end of the main shaft opposite the spring cylinder to measure the angular displacement of the shaft and valve disc.
Angular Velocity A Schaevi tz Model 7L6VT-Z linear velocity transducer (LVT) is mounted to the main shaft through a rack and pinion connection close to the RYDT to measure the angular velocity of the shaft and valve disc.
Differential Pressure in the Spring Cylinder A Va1 i dyne Model DP15 di fferenti al pr essure transducer is connected across the upper and lower parts of the spring cylinder to measure the differential pressure produced by piston motion in the cylinder.
Strain Measurements Micro-Measurement type CEA/350 ohm strain gages are used to measure strain at the locations listed below. A description of the position, orientation and purpose for each gage has been included along 7.1
TABLE 7.1 Measurements and Measurement Requirements for Testing of Anderson, Greenwood E Co.
Wetwell to Drywell Vacuum Breakers Accuracy, Frequency Mea sur emen t Range XFS Bandwidth
- 1. Valve disc 0.0 rad to angular position 1.2 rad 50 Hz
- 2. Valve disc angular velocity L 30 rad/se 50 Hz
- 3. Valve differential pressure 300 psid 50 Hz 4, Strain ~ 40 KSZ 1000 Hz 7.2
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I6 Datum 9300 Figure 7.1 AGCo vacuum breaker: phase IV test program instrumentation schematic 7.3
with several sketches showing the locations (not all gages were used in every test).
a) Ring Flange - one gage located 4 in. in from the outside diameter (OD) on the flat (back) face at the top, oriented radially (see gage No. 1, Fig. 7.2). Information from this gage is used together with the computer model to infer the stresses and strains throughout the ring flange.
b) Ring Flange - same as No. 1 above, but located at the bottom (see gage No. 2, Fig. 7.2). This gage, together with gage No. 1,demonstrates the type of load distribution at impact.
c) Ring Flange - one gage located 3/16 in. in from the OD on the back surface at approximately the bottom, oriented along the circumferential direction (see gage No. 3, Fig. 7.2).
d) Backplate - one gage located 3> in. in from the OD of the backplate on the back (visible) surface at the bottom, oriented radially (see gage No. 4, Fig. 7.2).
e) Dome - one gage on the outside surface of the dome just above the weld to the column, oriented radially (see gage No. 5.
Fig. 7.3), used to measure critical dome stresses.
f) 8 g) Dome - a biaxial gage located approximately 5 in. up from the center of the column. One gage is oriented radially, the other circumferential ly, (see gages No . 6 5 No. 7, Fig. 7 .3) .
h) Arm Assembly - one gage located just above the turnbuckle on the face of the arm further from the dome, oriented along the axis of the arm (vertically in the closed position) (see gage No. 8, Fig. 7.4). It is used to determine stresses in the arm and to infer stresses in the turnbuckle, keys and portions of the main shaft.
i) Main Shaft - two gages located on the main shaft just outside of the bearing on the linkage side 180 apart with longitudinal orientation to measure the bending moment in the main shaft (see gages No. 9A 8 Ho. 9B, Fig. 7.5).
j) Linkage - one gage located on the edge of the link connected to the main shaft, oriented parallel to the length of the linkage, (see gage No. 10, Fig. 7.4).
k) Main Shaft - two gages located on the main shaft just outside of the bearing on the linkage side at 45 to the axis of symmetry and at 90o with respect to each other to measure the torsional-moment in the main shaft (see gages No. 11A 8 118, Fig. 7.5).
- 1) Main Shaft - two gages located on the main shaft just outside of the bearing on the linkage side 180o apart (90o apart from gages No. 9A 5 No. 9B) to measure the component of the bending moment in the main shaft orthogonal to that measured by gages No.
9A 8 No. 9B (see gages No. 12A 8 No. 12B, Fig. 7.5).
m) Linkage - one gage on the neutral axis of the link to measure force in the link (see gage No. 13, Fig. 7.4.).
7.4
n) Cable Link - one gage on a link connecting the column at the center of the disc to the cable/actuator system to measure tension.
7.5
STRAIN FEE LICIT!ONS (Liver)ch Valve) 01 (on a<n9 van~)
1 2" Ou.side radius of Ring Flange
/ III Outside radius of Radius of Back Plate Col w n 3-1/2" N2 P3 3/)6" 1/2" BACK Vl &(
(Not to Scale)
Figure 7.2 Strain gage locations (Limerick valve): gages Nos. 1-4 7.6
STRAI tt aA6K tDGATlNs (L)aerick Ya1vt)
I I
I
~es I lg7 Note: Gages 6 8 7 can be replaced by a single Bi-axial Gage I I
l Radius of Dof-:e I 5 II I
I I
Radius of Col@an FRONT VIBf (Not to Scale)
Figure 7.3 Strain gage locations (Limerick valve): gages Nos. 5-7 7.7
A Rain Shaf t tt Sprlnp S)de) iear$ np {$
Q 410 Qv~
~ Tur nbuckle (No Scale)
To Dome Assembly STRA1N C4GE LOCATIONS (Limerick Valve)
Hain Shaf t jo SECTlON A-A (No Scale)
To Dome Strain locations (Limerick valve): gages Nos. 8-10,13 Figure 7.4 gage 7.8
STRAIN GAGE LOCATIONS ON MAIN SHAFT TOP VIEW 12B
)
\
C.
-1:l 12A 9A,llA 9A 11A 12A 12B 12A J
9B,11B 9B 1YB SIDE VIEW END VIEW 9A,9B Measures most of the bending moment with the disc full closed 12A,12B Measures most of the bending moment with the disc full open llA,llB Measures strain due to torque Figure 7.5 Strain gage locations on main shaft: gages nos. 9A, 98, llA, aaB, 12A and 128
8 OUALITY ASSURANCE All controlled activities were performed in accordance with the test procedures specified in the C.D. I. guality Assurance Manual. Controlled activities are those .which are directly related to the planning, execution and evaluation of tests intended to produce data necessary to evaluate stresses or validate models. Supporting activities such as test apparatus design, fabrication and calibration and tests designated with an "X" in the test number by the principal investigator are not controlled by the C.D.I. test procedure or the referenced guality Assurance Manual.
Fig. 8. 1 is a schematic of the C.D. I. guality Assurance Program for
.testing. In addition, the instrumentation certification and the calibration, testing and data reduction procedures, as well as actual test results are contained in the C.D. I. design record file (Ref. 4).
8.1
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APPENDIX A Valve Drawings
9 REFERENCES
- 1. Letter from H;C. Pfefferlen, Manager of BWR Licensing Programs, General Electric Company to T.P. Speis, Assistant Director for Reactor Safety, Nuclear Regulatory Comnission. Letter Reference MFN-098-82 dated July 23, 1982.
- 2. "Mark II Containment Drywell-to-Wetwell Vacuum Breaker Models,"
General Electric Company Report No. NEDE 22178-P, August 1982.
- 3. "Dynamic Testing of AGCo Wetwell-to-Drywell Vacuum Breakers, Phases I 8 II." Continuum Dynamics Inc. Tech Note No. 82-27 in preparation.
- 4. Continuum Dynamics, Inc. Desi gn Record File B-054 prepared for Bechtel Power Corporation under Technical Services Agreement 8031-M-169.
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