ML20032B669

Forwards Tes 3147, Sentinel 1S Radiation,Structural & Thermal Evaluation, as Application for Amend to Certificate of Compliance 9153

ML20032B669
Person / Time
Site:	07109153
Issue date:	10/21/1981
From:	Roger Hannah TELEDYNE ENERGY SYSTEMS
To:	NRC OFFICE OF NUCLEAR MATERIAL SAFETY & SAFEGUARDS (NMSS)
References
19837, S-RGH-229, NUDOCS 8111060032
Download: ML20032B669 (9)

Text

9PTELEDYNE ENERGY SYSTEMS 110 W. TIMoNIUM RD.

TIMONIUM. M D. 21093 PHONE: 3012524220 TELEX: 8 7780 CABLE: TELISE' 21 October 1981

,3 ;; g,; i Refer to: S-RGII-229 U$Y d WU e 39/.S5 0 )~ %

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8/g Mr. Charles E. MacDonald, Chief Transportation Certification B; anch N

S Division of Fuel Cycle and Material Safety Nuclear Regulatory Commission g

6 Washington, D. C. 20555

'O

Subject:

Amendment to Certificate of Compliance Application, Docket No. 71-9153 Gentlemen:

Teledyne Energy Systems herewith submits an amend.nent to our license application, TES-3147, " Sentinel IS Radiation, Structural and Thermal Evaluation. "

The enclosed ten packages of seven pages each, replace pages 2-22 through 2-24 of Section 2. 7.1 " Free Drop," submitted previously.

Sincerely,

/

/

Ilannah f/

/

) Terrestrial Power Systems j

,,B o am Manager F 0 N

,C4 9 198 k e dw

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Enclosures:

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19837 P'Re8Waisni, PDR

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SUBJECT:

DISTRIBUTION OF CHANGE - PAGES 2-22 thru 2-2-1,d SENTINEL E RADIATION, STRUCTURAL AND THERMAL EVALUATION TES-3147 O

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An impwt of the generator on its side is similar to the case above where some of the availabic energy is converted to strain energy of the 3lin-K insulation. In reality O

the coelina tin, wiii attain an ineiabliity and abserb eignificant etrain enerer in bending.

For this analysis the latter energy dissipator will be ignored. It can be shown that for this orientation, the minimum crush-effective volume of insulation is about 27.3 in.3 At 9. 5 in-lbs/in.3 the strain energy is 230 in-lbs.

A similar situation exists for an impact on the top or upier end of the generator with the exception that there is no effective volume of insulation for that direction.

For this orientation, the material between the housing and shield is the thermoelectric mcxlule, a relatively brittle semiconductor alloy providing negligible strain energy.

For both the side and top impact there is no concern for the shield lid bolts. From Figure 2. 7-4, it is shown that the shield lid protrudes well into the shield cavity such that bolt deformation is limited in the shear plane corresponding to the side impact orientatio'i. For the upper end impact the bolts are not loaded beyond their initial torque.

The radiation shield, fabricated from uranium - 3/Cc titanium, is evaluated for direct impact response for two attitudes, side-on and top end-on. For both orientations energy is absorbed in bending of the cooling fins that are integral with the housing that surrounds the shield. It can be shown that the energy absorbed in bending is approx-imately 4000 in-lbs in each direction. Ilowever, this magnitude is insufficient since the available energy associated with a 50 lb shield and fuel capsule dropping 30 feet is, 50 (30) (12) = 18,000 in-lbs E

=

Conservatively assuming that the shield impacts a rigid surface with no loss of energy due to surrounding structure, a shock rise time is derived and the resulting stresses are obtained. From the reference cited below,* the peak deceleration is obtained from the equation, f

G

=

deceleration, g's where:

G

=

shock rise time, milliseconds t

=

h

= drop height, inches For an impact on a flat face the shock rise time for rigid steel against concrete is one (1) ms. This value should be slightly larger when impacting U-3/4 Ti since its modulus is 2G x 106 psi versus 20 x 106 psi for steel. It is also important to note that an impact against an edge or point the shock rise time is greater which implies lower deceleration. For t = 1 ms,

• Heference 6: " Design for Shock Resistance " by H.T. 31sgner, Product Engineer *ng, 1902.

O TES-3147 2-22

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For the end-on (top) i;apact the maximum stresses can be easily derived.

. At the upper hurface of the lid, the inedia force-is, P,=

13G0 (2. 85 + 30. 95 + 1. '19 + 9. 25)

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=,. p (2. 705)~ = 5. 7 47 in~

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5.717 The stainless steel ring has a minimfim yield strength of 30,000 psi. The min-imum area is, o

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The inertia force 1.s 13GG (3G. 98 + 1. 29) = 52277 lbs. Therefore, the stress is, O

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- g 43g For the side-on impact the potential failure of the lid is in ahear. The effective weight is, g - (3. 955)" (1.10

. 295)-

= 7.79 n

. 672 ( +-- (2. 705)'t. 295) +

W

=

130G (7. 79) = s 10G11 fin P

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The inertia forces in the shield body are approximated by examining a section of unit length. The ANSYS finite element program was utilized where the thick walled circular section was modeled by 72 elements as shown in Figure 2.7-5.

Each element Q

is an isoparametric solid defined by four nodal points having two degrees of freedom at V

cach node point, translations in the x and y directions. The tractions are based upon 1360 g's acting on the mass of each element in the -y direction. The total force is reacted as a line load at node 84. The resultinc stresses are conservative since the constraints provided by the lid and lower end closure are neglected. The material properties of interest for the U-3/4% Ti include E = 2G. 0 x IOG psi, v = 0. 3 and

. 672 lbs/in3, 9

=

The stress distributions ofinierest are located at O = 0, 90 and 270*.

a.

At 0* (elements 1 and 2) the stress distribution across the wall is the superposition of benling and compression as shown below.

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b.

The maximum tensile stress occurs at R =. 040 inch aul 9 = 00*.

The V

. alue is C070 psi.

c.

The maximum stress occurs at tn" line of contact with the impacting surfar n (node 8') of element 54. At this location there is a compressive strest (-13,001 psi) due to bending, a compressive stress in the y-<lirection

(-10,735 psi) and a shear component. The resulting equivalent stress is 26,831 psi.

The stresses derived, however, are a result of an equivalent static loading.

The loads are not static but realistically are a result of a time dependent impulse. The actual response is a function of the shock period and the fundamental frequency of the body receiving the impulse. The shock pulse can be repr>;sented by a half-sine wave.

Ilowever, although the shock rise time and the amplitude are known, the total duration of the pulse is not known. For this reason, the maximum potential amplification factor of 1. 78 is applied. Table 2. 7 -1 presents the " static" stresses derived, the " dynamic" stresses and the latter is compaled to the yield stress of the material oiinterest.

The shield in a structural sense is essentially a solid block. That is, the volume of the cavity receivhig the fuel capsule and fuel is very small relative to the volume of actual material. The effective volume is 8G7c. In every way, the shield must be con-sidered " thick walled. " Without aralysis the only conceivable plastic deformation en-visioned would be a slight coining of an exterior edge.

2.7,2 Puncture v

The second hypothetical accident condition in the sequence pertains to a free drop of 40 inches onto a stationary and vertical mild steel bar of G inches diameter with its top edge rounded to a radius of not more than 1/4 inch. As in the previous analysis, for the 30-foot drop, the applicable configuration addressed includes the shield and the encapsulated fuel. The structural capability of the cask is ignored.

Since the mild steel bar diameter is nearly equal to any dimension (i.e., length, dia-meter, etc. ) of the shield, potential penetration is impossible. The response would be identical to the impact from a 30-foot drop with the exceltion that the available energy would be considerably lower.

TES-3147 2-24.c

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O TABLE 2. 7-1 COMPARISON OF CALCULATED STRESSES WITII YIELD AND ULTIMATE STRENGFIIS Maximum Dynamic Yield Ultima'e Impact Static biress Stress Sirength Strengt h Orientation Stress Location (psi)

(psi)

(psi)

(psi)

Top Upper surface of lid

-11072 21310 50000 128000 Top Stain 1 css steel ring

- 5528 08.10 30000 75000 Side Shear of lid 3761 GG95 7G800*

4 Side Side 2G831 47759 50000 128000 Y$

25 "5

• The ultimate shear stress is approximated as 007o of the ultimate tensile stress.

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