ML20004E652
| ML20004E652 | |
| Person / Time | |
|---|---|
| Site: | 07109144 |
| Issue date: | 04/21/1981 |
| From: | Reynolds L CHEM-NUCLEAR SYSTEMS, INC. |
| To: | Macdonald C NRC OFFICE OF NUCLEAR MATERIAL SAFETY & SAFEGUARDS (NMSS) |
| References | |
| 18996, NUDOCS 8106120435 | |
| Download: ML20004E652 (15) | |
Text
-
CHEM-NUCLEAR SYSTEMS INC.
.O.
P.O. Box 1866 e Bellevue, Washington 9 e 406) 827 0711
- /
s h
u a ma
~
6; APR 2 71981 *.T3 pg,gg
.3.s.nuctanamuwon -
cov'g*
April 21,1981 9
vaasc>w 0
\\
e 6
Charles E. MacDonald cecwt s Transportation Branch p
us9C
{\\
g>'i 3 g gg8\\ *
~
Division of Fuel Cycle &
Material Safety p<.
U. S. Nuclear Regulatory Commission 1
ess [ttu e
S 9g;i Washington D. C. 20555
Reference:
Docket No. 71-9144
Dear Mr. Mac. Donald:
We are submitting herewith our repis to the various questions which we have discussed during recent telephone conversations. We trust that this submittal will permit you to make an early determination on our application for a Certificate of Compliance for the SGC-1 package. A revised list of effective pages is enclosed.
Please contact us if you have any questions in this matter. We will appreciate ycur prompt attention.
W I~
Sincerely, EM-NUCLEAR SYSTEMS, INC.
b gi9
(
.M i63 M L is E. Reynold.;
d
,,s.
Director Regulatory Affairs
\\S
/h I
- V LER:slj Enclosure Q "[
1.ee-.y 3 A k.
...., 5 i
% 7hD N
8106120MS6 c
TABLE OF CONTENTS (Continued) s Page 2.4.4.1 Barge Tiedown System 2-13 2.4.4.2 Trailer Tiedown System 2-33 2.4.5 Internal Contents Tiedowns 2-37 2.5 Standards for Type B and Large Quantity Packaging 2-45a
$3 2.6 Normal Conditions of Transport 2-46 2.6.1 Heat 2-46 2.6.2 Cold 2-46 2.6.3 Pressure 2-46 2.6.4 Vibration 2-47 2.6.5 Water Spray 2-57 2.6.6 Free Drop 2-59 2.6.7 Corner Drop 2-87 2.6.8 Penetration 2-87 2.6.9 Compression 2-87 2.7 Hypothetical Accident Conditions 2-87 2.8 Special Form 2-87 2.9 Fuel Rods 2-87 2.10 Appendix 2-87 2.10.1 Tiedown Criteria Discussion 2.10.1-1 2.10.2 STARDYNE 2.10.2-2 3.0 THERMAL EVALUATION 3-1 3.1 Discussion 3-1 3.2 Summary of Thermal Properties of Materials 3-1 3.3 Technical Specification of Components
?1 3.4 Thermal Evaluation for Normal Conditions of Transport a-1 3.4.1 Thermal Model 3-2 3.4.2 Maximum Temperatures 3-2 3.4.3 Minimum Temperatures 3-2 3.4.4 Maximum Internal Pressures 3-2 3.4.5 Maximum Thermal Stresses 3-3 3.4.6 Evaluation of Package Performance for Normal Conditions of Transport 3-8 3.5 Hypothetical '..cident Thermal Evaluation 3-d 3.6 Appendix-Then.ial Analysis 3-9 Figure 3-1:
Steam Generator / Cask Thermal Model 3-11 Figure 3-2:
Ther...al Resistor Model 3-13 Figure 3.6.1 Cask Segment Heat Loads 3-18 Figure 3.6.2 Node Temperatures for SGC-1 3-21 4
CONTAINMENT 4-1 ii Revision 3 April,1981
TABLE OF CONTENTS (Continued)
Page 9.
QUALITY ASSURANCE 9-1 I
9.1 Appendix 9-2 Approval Letter for CNSI Quality Assurance Program 9-3 NRC Form 311 9-4 Appendix A Response to NRC Request for information date
.12/18/81, Docket 71-9144 A-1 2
Appendix B Accident Discussion B-1 Appendix-C. Dynamic Response C-1 13 l
I
\\
i i
a I
L Revision 3 IV
- Aoril, 1981 9-"*
--mh
- e-g-g--
p 9*,*e wyw, o w swp.-,_.myy.wwyy 7
+-pwgpwm---
9-pgg-*94yetmy gyy 9
mp wp p9-p-e_-
wm--egyq %
A.we s-9 7.--atm9wyqy49%
g
EETECTIVE PAGES (CINr.)
t PAGE g
2-9 January 1981 2-10
=
2-11
=
2-12 2-13
=
2-14
=
2-15 April,1981 3
2-16 January, 1981 2-17 2-18 a
2-19 2-20 a
2-21
+
=
a 2-22 2-24 a
a 2-25 a
2-26 2-27
=
2-28 a
2-29 a
2-30
=
2-31 a
2-32
=
2-33 a
2-34 a
2-35
=
2-36 a
2-37 a
2-08 a
2-39 a
2-40
=
2-41 a
2-42.
a 2-43 Rev. 3, April, 1981 vi p
~ - -
9,"n, w
-w
$3 + er p
'T7'*9'"*'*-'-W4-
- -7""''Y lf-'W'w4NN yVW-*-gr+'***'-
w e*t-"-'w7"w' t-M-%T~-v'"M-WW-*= ' "-"et-"-W*'*'wW 9-'t"T-t pr-
-.=
.~.
EFFECTIVE PAGES (CONT.)
PAGE DATE 7-2 March 1981 i '
January 1981 9_1 A-1 A-2 A-3 A-4 A-5 2.10.1-2 March 1981 2.10.1-3 2.10.1-4 7-3 u
7-4 II 7 n iv i
i H
t v
u viii n
ix April, 1981 3
B-1 March, 1981 B-2 H
B-3 i.
B-4 u
i B-5 1
vi April, 1901 2-45a 2-45b 2-45c 2-46 C-1 C-2 C-3 C-4 C-5 ii
~
ix Rev. 3, April, 1981 A
w
.g
- N%wi*rr*%erJ' s
4 r
h%
$+h;.
o\\
k IMAGE EVAi.UATION Y
TEST TARGET (MT-3) i 1.0 5In EM e5 Ea u ILt 1.13d'"EE
+
/
,4 1.25 1.4 1.6 f
+r b,
+ sp i
4 +k,,,$
'$d,};.[
1 4
}
j
-ill l
c; u
g' f
//
c-IMAGE EVALUATION l TEST TARGET -(MT-3) f
'il I.0 gin m
(
k
= g g Ea 1.l \\i = EE 1
~
/
!M i 1.25 i
1.6 I
. l 1.4-f 99 y
c 4#ff rp p4%\\
k 7,,,77 g.1}#b A
f 7
l
+
,y n
l
\\\\\\\\/
r.ii,;s
+4,,+
4-l MAGE EVALUATION
\\
. TEST TARGET (MT-3)-
i 1.0 gnu na
-[ l[IMA v
qnu=m
/
3 4..
125 g gig j :/
4 6"
$$[# D/>;,,4,b,'
?<Q;(4 4 //4N\\\\
W 7,
i
i
,7_
/'
m smas
-EcaY 1
- ;t
/,/
r
/
'/'
/
s
,/
)
_4
== J EM
//
i
/
i.
4 i,/
V 55%%)
)
/
\\
r'
/+
~
q v
a = 121.625 e = 67.75 j =.92'.375
.m = 8,2.875 -
l3 b = 91.75 f = 86.81 k = 121.625 p = 104.86 c = 52.56 g = 110.'12 1 = 161.9I d = 161.16 h = 53.75 n = 64.25 BARGE TIE DOWN SYSTEM FIGURE 2.4.4-1 j
Apri k981 2-15
4 2.5 Standards for Tyoe B and large Quantjt,
__g : aging
~
2.5.1 Load Resistance The cask if treated as a simple beam supported at its ends, can support a uni-formly distributed load equal to five times its fully loaded weight.
Five times loaded weight = (5) 722,000
= 3.61 x 105 lbs.
Length = 41 ft. 6 in. (excluding flanges) 3
= 498 in.
Load /in. = 7249 lb/in = w h
a=
For uniform load WL 7249(494)2 2.247 x 10e M=
=
=
8 8
For conservatisre assJme the cask is a right cylinder of the small diameter.
I = n /64 (D" - d") = n 1/64(149" - 144")
= 3.088 x 105 8
a = 2 247 x 10 (74.3) = 5422 psi 3.088 x 105 MS = 3800
-1 6.0
=
5422 I
i Revision 3 l
Page 2-45 a April 1981 W
N 2.5.2 External Pressure The SGC-1 package will suffer no loss of contents if the package is subjected to an external pressure of 25 psig.
Hoop stress a = gr t
Assume cylinder of the largest diameter found on the cask D = 170 in r = 85 in,
f Un = 25(85) 850 psi
=
2.5 M.S. = 38000
-1
= + large
~
850 The end plates can be modeled as a semi-circle with fixed edges.
From Roark and Young, " Formulas for Stress and Strain" 5th ed., McGraw-Hill, Table 24 page 371.
Page 2-45 b Revision 3 April 1981
a max. =
-0.42 o a2 2
t q = pressure a = radius t = thickness a max. = 0.42(25)(85)2 -
27586 psi compression
=
2.75 M.S. = 38000
-1
+.38 27586 If considered one uniform plate o=6M M
qa
= 22578 in.lbs.
2 '
2 t
8 o=
6(22578)
-1 2.12
=
^
(2.75)2 The cask will adequately react 25 psig external pressure withcut loss of contents structurally.
The gasket is a full face flange gasket. The greater the external pressure on the shell the greater the gasket seating pressure and less likely the gasket is to leak'.
m Revision 3 Page 2-45 c April 1981
O J
m 2.6 Normal Conditions af Transport The Mcdel SGC-1 packaging has been designed and the contents are so limited (described in Section 1.1.2 above) that the performance requirement ~ specified in 10 CFR-71.35 will be met when the package is subjecte. to the normal conditions of transport specified in Appendix A of 10 CFR 70 with the exception that the free drop will not be met due to the lack of applicability.
The ability of the Model SGC-1 packaging to satisfaction withstand the normal con-ditions of transport has been assessed as described below:
2.6.1 Heat The thermal evaluation for the analytical thermal model is reported in Section 3.4 2.6.1.1 Summary of Pressures and Temaeratures With a maximum solar heat load in 130oF air, the external maximum' temperature rose to 168.70F and the internal temperature rose to id90F with an internal pressure of 5.49 psig.
These conditions had no detrimental effect on the package.
2.6.2 Cold The materials of construction in this package as described in Section 2.3 have the ability to withstand a standard Charpy V-notch test with a minimum of 15 ft-lbs impact energy at -400F.
Based on that criteria, it is safe to conclude that cold will not substantially reduce the ef-fectiveness of the package.
2.6.3 Pressure i
A differential pressure e#.5 atmosphere will be reacted by the cask and its closures.
Loads on the closure bolts are l
calculated as follows:
The longitudinal stress and maximum hoop stress in the cylinder are:
fh = PR/t = 14.7/2 (85/2.5) = 249.90 psi fl = PR/2t = (14.7/2) 85/(2)2.5 = 124.95 psi l
Assuming these biaxial stresses are additive.
fmax = 374.85 psi Revision 3 2-46 April, 1981
APPENDIX C DYNAMIC RESPONSE OF THE MARINE TIEDOWN SYSTEM The cask with its contents is secured to the trailer. This complete system is secured to the barge by 16 tiedowns as shown in figure C-1 and figure 1.3.3-10.
To determine the time dynamic response of the system would require a detailed and complex model. An approximate response can be determined by looking at the system as a lumped mass system with three hypothetical springs representing the summation of the spring forces of the tiedowns.
This model is ba,ed on several assumptions:
1)
The combined mass of the steam generator, the cask and the trailer can be lumped as a single mass.
3 2)
The mass described in 1) is a point mass.
3)
The barge beneath the trailer has the same spring coefficient as the vertical components of the tiedowns.
4)
The tiedown components in the plane of the barge on opposite sides / ends of the cask act equally and opposite.
5)
The order of magnitude of the natural frequency of the system is not affected by the coupling terms.
6)
The tiedowns are considered massless in relation to the cask and trailer.
(Each tiedown weighs less than 3000 lbs.)
7)
The barge connections are considered rigid.
8)
The relative position of the barge /tiedown connections are considered fixed in relation to one another.
The above assumptions permit the system to be modeled as a mass and three springs as shown in figure C-2.
This results in the following simplified equations of motion:
mi+kx=0 x
m"
+ky=0 m
+kz=0 Defining the terms:
M = combined mass of the steam generator, the cask and the trailer =
d sed
.6#B in 2X
=
(
2 t/ c 12 in./ft.
C-1 Revision 3 April 1981
ee.
\\
LR Ns\\ '
NA\\
1 e
/
1-(\\
La
'y
[ ATERA L N*5
N L ousiruaina t.
56 x
\\
s
/~
Figure C-1
/DE 3
Km D
Y y Figure C-2 C-2 Revision 3 April 1981
For a bar X AE
= (
metal area A
=
modulus of elasticity E
=
length L
=
T%e tiedown can be considered actually three springs, two end springs that are identical and a spring representing a take-up rod.
The ends are approximately 39 inches in length, with a metal surfacg area of about 60 square inches and a modulus of elasticity of about 29 x 10 psi.
.ne rod varies in length from approximately 14.5 active inches in length for.ne lateral tiedown to about 56 active inches in length for the longitur' tiedown.
The threaded rod is 41 inches in diameter with a stress area of about 13.8 square 6
inches. The modulus of elasticity for the rod is about 29 x 10 psi.
6 4.46 x 107 (60) (29 x 10 )
16/in.
A KE
=
=
=
LE 39 3
6 (13.8)(29 x 10 )
7 AR ER Kr' lateral
=
2.76 x 10 lb/in.
=
L 14.5 R ateral l
An En (13.8)(29 x 10 ) = 7.15 x 106 6
lb/in.
Ko, lor.gitudinal
=
=
LR1ongitudinal 56 K
I 7
1.23 x 10 lb/in.
lateral
=
=
L+L+L KE KE KR ateral 1
K 1
0 longitudinal
=
5.41 x 10 lb/in.
=
__1 + L + L KE E
K KR ong.
i From figure 2.4.4.1 the tiedowns can be resolved into components in the x,h,z directions.
In the x and y directions, only one-half of the tiedowns are react-ing since the tiedowns are hinged allowing only tensile loads.
5 7
= 1.63 x 10 lb/in.
K Klong. " 4 Klong.
1 l.
=
x K
- 4K 7
Ky
=
lat.
long.
i 6+4Klat.
b 12 = 5.11 x 10 lb/in.
C-3 Revision 3 April 1981
,,. _. -, ~..
In the vertical direction all tiedowns react upward, and the barge deck reacts the dcwnward movement.
8K
+8K
= 7.08 x 107 lb/in.
K KZ vertical long. 6i 6 lat.
6 2
=
From the uncoupled equations of motion:
[
h
= 84.93 rad /sec 13.52 cycles /sec
=
=
e1
=
- [
[
= 149.48 rad /sec "2
23.79 cycles /sec
=
=[]x
= 177.00 rad /sec
=
W3 28.17 cycles /sec
=
x The forcing functions are the pitch, heave and roll of the barge. The period for j
the pitch and roll is about 20 seconds (ANSI 14 N 522.) This results in a fre-quency of.05 cycles /seccad. Another impulse force is that induced by slams.
From "A Study of the Single Voyage Risk Levels Associated with Extreme Motion Values for Voyage from Norfolk, Virginia, to Astoria, Oregon," L.R.
Glosten &
- es,
nc., the maximum slam frequency is 86 slams per hour. This 2r frequency than the other periodic loadings.
results in...
The magnification factor that results from the forcing function is:
MF 1
=
1 MF 1
1
=
=
1.05
<2 1313.52[
The natural frequency of the system is considerably higher than any of the forcing frequencies.
i It is recognized that the values given above are not the true natural frequencies of the various modes of the system. However, the values given represent relative orders of magnitude of the system. Even if the true natural frequency of the l
system was two orders of magnitude less than the calculated, the magnification factor would be on the order of 15%.
The damping of the system is large. The assumption that the barge is rigid is very conservative because the barge flexture will dampen the system. Also, any i
motion of the barge is dampened by the sea. However, if one can assume the barge to be rigid in relation to the tiedowns, the cask itself is further dampened by I
i i
l C-4 Revision 3 April 1981 w---y-ip m.
wvy-
friction. Treating the cask as a body with Colamb dampening due to
^
friction, the minimum friction force which prev 2nts vibration at resonance is:
.79 Ku Ff
=
o spring constant in the direction of motion where K
=
displacement in ua
=
C.M. Harris &
C.E. Crede, Shock and Vibration Handbook, 2nd ed. McGraw Hill, 1976. Page 30-8.
On the deck of the barge the cask generates the following frictional force, assuming the coefficient of friction between wood and steel to be equal to.4.
Ff 872,000 (.4) 348,800 lbs.
=
=
This gives a maximum displacement of 348,800
.01 in*
=
ua
(.79)(5.11 x 10/) =
Assuming that the majority of the elongation occurs in the tie rod, the required loading can be calculated for the longitudinal or longest tiedown. From section 3
2.4.4.1 page 2-22 Q, 435310 (56) -
PL
{'
u0
- 06 in*
=
=
13.8 29 x 10o for 1.5 loading.
g The.01 in displacement is equivalent to:
1.5
.01)
.25 g loading.
P
=
=
g From the L.R. Glosten report it is evident that the high accelerations are in-frequent and random. The damping of the system would prevent resonance amplifi-cation of the higher frequency loadings.
In conclusion, the rigidity of the tiedowns create a considerably higher natural frequency for the system than the expected forcing frequencies. The system as a whole is dampened so that only the higher accelerations will cause vibration.
C-5 Revision 3 April 1981 18306
..