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European Atomic Energy Community - EURATOM abi *
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FIAT SpA, Sezione Energia Nucleare -
Società ANSALDO SpA - Genova
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FORCED CONVECTION BURNOUT AND
HYDRODYNAMIC INSTABILITY
™ " EXPERIMENTS f
FOR WATER AT HIGH PRESSURE Part IV : BURNOUT EXPERIMENTS IN A DOUBLE CHANNEL TEST
SECTION WITH TRANSVERSELY VARYING HEAT GENERATION
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A. CAMPANILE, G. GALIMI and M. GOFFI
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1968
(SORIN, Centro Ricerche Nucleari, Saluggia-Italy)
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LEGAL NOTICE
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This document was prepared under the sponsorship of the Commission of the European Communities.
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,i!í^'M'!ffi Neither the Commission of the European Communities, its
contractors nor any person acting on their behalf :
Make any warranty or representation, express or implied, with respect to the accuracy, completeness, or usefulness of the information contained in this document, or that the use of any information, apparatus, method, or process disclosed in this document may not infringe privately owned rights ; or
i Assume any liability with respect to the use of, or for damages
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EUR 3881 e F O R C E D CONVECTION B U R N O U T A N D H Y D R O D Y N A M I C I N S T A BILITY E X P E R I M E N T S FOR W A T E R A T HIGH P R E S S U R E P a r t IV : B U R N O U T E X P E R I M E N T S IN A D O U B L E CHANNEL·
T E S T SECTION W I T H T R A N S V E R S E L Y V A R Y I N G H E A T G E N E R A T I O N
by A. C A M P A N I L E , G. C A L I M I and M. G O F F I (SORIN, Cent ro Ricerche Nuclear i , Sa luggia — I ta ly ) European Atomic E n e r g y Communi ty — E U R A T O M F I A T SpA, Sezione Energ ia Nucleare — Torino Società A N S A L D O SpA — Genova Cont rac t No. 008-61-12 P N U Brussels , F e b r u a r y 1968 — 36 P a g e s — 13 F igu res — F B 50
Expe r imen t s have been carr ied out on a complex geomet ry test section consis t ing of two h e a t i n g rods coaxially mounted in two adjacent and communica t ing flow channels .
EUR 3881 e F O R C E D CONVECTION B U R N O U T A N D H Y D R O D Y N A M I C I N S T A BILITY E X P E R I M E N T S FOR W A T E R AT HIGH P R E S S U R E P a r t IV : B U R N O U T E X P E R I M E N T S IN A D O U B L E C H A N N E L
T E S T S E C T I O N W I T H T R A N S V E R S E L Y V A R Y I N G H E A T G E N E R A T I O N
by A. C A M P A N I L E , G. GALIMI and M. G O F F I ( S O R I N , Cent ro Ricerche Nuclear i , Sa luggia — I ta ly ) European Atomic E n e r g y Communi ty — E U R A T O M F I A T SpA, Sezione Energ ia Nucleare — Torino Società A N S A L D O SpA — Genova Cont rac t No. 008-61-12 P N U Brussels , F e b r u a r y 1968 — 36 P a g e s — 13 F igu res — F B 50
Expe r imen t s have been carr ied out on a complex geome t ry test section consis t ing of two h e a t i n g rods coaxially mounted in two adjacent and communica t ing flow channels .
Several conditions of differential heating in the two channels were tested to the aim of investigating the effect on burnout limits of possible variations of local flow velocity and fluid enthalpy due to transverse flow redistribution and mixing.
Several conditions of differential heating in the two channels were tested to the aim of investigating the effect on burnout limits of possible variations of local flow velocity and fluid enthalpy due to transverse flow redistribution and mixing.
EUR 3881 e
European Atomic Energy Community - EURATOM
FIAT SpA, Sezione Energia Nucleare - Torino Società ANSALDO SpA - Genova
FORCED CONVECTION BURNOUT AND HYDRODYNAMIC INSTABILITY
EXPERIMENTS FOR WATER AT HIGH PRESSURE
Part IV : BURNOUT EXPERIMENTS IN A DOUBLE CHANNEL TEST SECTION WITH TRANSVERSELY VARYING HEAT GENERATION
by
A. CAMPANILE, G. GALIMI and M. GOFFI (SORIN, Centro Ricerche Nucleari, Saluggia-Italy)
1968
Contract No. 008-61 -12-PNII
SUMMARY
Experiments ha\-e been carried out on a complex geometry test section consisting of two heating rods coaxially mounted in two adjacent and communicating flow channels.
Several conditions of differential heating in the two channels were tested to the aim of investigating the effect on burnout limits of possible variations of local flow velocity and fluid enthalpy due to transverse flow redistribution and mixing.
KEYWORDS
HEATING ENTHALPY BURNOUT VELOCITY MOCKUP COOLANT LOOPS FLUID FLOW TESTING
TABLB DES HATIÜEES
Page
1. Introduction 5 2. Test section 5 3. Control of the subchannels geometrical symmetry . . 8 4. Burnout experiments 10
4.1* Hange of parameters 10 4.2. Burn-out data presentation 10
5. Bemärks 11 Bibliography ^
rOKCED CONVECTION BURNOUT AND HYDRODYNAMIC INSTABILITY EXPERIMENTS FOR WATER AT HIGH PRESSURE^*'
1. Introduction
The flow passage of an open lattice core, with rod bundle type fuel elements, consists of non circular channels bounded by fuel rods each having connections with the neighbouring channels through the gap between the rods.
Several factors may contribute to set-up non uniform transverse conditions in a matrix of fuel rods and coolant channels, namely:
- Radial flux distribution - ilux peaking - Dimensional tolerances and deformations - Fuel loading variations - Inlet flow differences - Presence of non fueled reis (cluster centrei).
To the purpose of investigating possible influences of transversally unbalanced conditions existing in adjacent chan neis an experimental study has been carried-out by SORIN under the research and development contract between EURATOM-FIAT and Ansaldo for nuclear ship propulsion.
The experiments were performed on the SORIN pressurized water loop described in detail in réf. /Î/·
Pig. 1 shows a schematic diagram of the loop .
2. Test section
The investigation on the influence of transverse shift of flow upon the burnout in subchannels of a rod cluster fuel
Manuscript received on December 12, 196?.
6 -
assembly, was performed in a test section consisting of two adjacent and communicating channels with provision for differential heating in the two channels.
Each channel had a heater rod in axial position. The perimetral conteur of the flow duct, hereafter referred to as the shell,was shaped as to simulate the configuration of the flow area associated with two fuel rods in a rod bundle (Fig. 2) . It was suitably designed to have heat generation practically in the curved section only of the containment wall.
This was achieved by brazing, in a controlled atmosphere furnace, four quarters and two halves of stainless steel tubes, 1 mm thick, to very thin stainless steel strips, 0.18mm thick.
The corrugation of the thin strips observed in the preliminary specimens ¿2/ was considerably reduced by improving the technique of fastening the various parts in the furnace.
Stainless steel discs were brazed at each end of the shell to allow connection to the electrical power connectors.
The heater rods consisted of two stainless steel tubes 10.2mm O.K., 1mm thick, internally provided with four thin stainless steel wires welded to the tube walls at the entrance, the exit, the mid point and 10 mm upstream of the exit end of the heated length. The wires were used as voltage taps for voltage drop measurement as well as for burnout detection by means of a bridge type detector .
The heater rods were centralized in each subohannel by pas sing them through positioning holes of an entry and exit grid plates. All the parts at different voltage were suitably in sulated by using sintered aluminium oxide rings.
In addition, to eliminate the risk for the rods to get in touch with perimetral walls, each of them was held in po sition by means of two sets of three adjustable ceramic pins at 120° located at 1/3 and 2/3 of the entire heated length (Fig. 3).
The heating current to the three resistors of the test channel,namely the two rods and the shell, was supplied from a d-c rectifier rated for 600 kW.
The rod purposely selected to be overloaded up to the burnout treshold, hereafter referred to as "burnout roa", was spring loaded to prevent it from bowing during the burnout tests.
In order to obtain present ratios of the shell and adjacent rod heat flux to burnout rod heat flux, provision was made to allow feeding of the heating elements at different voltage through a suitable setting of the variable resistors R.. and Rp (Fig. 4) ·
The electrical connectors were made of stranded oopper cable enclosed in flexible stainless steel corrugated tubes. This arrangement presented enough flexibility to leave the heated elements free to expand.
The channel, with the rods positioned in the end terminal grid plates, was enclosed in a thin cylindrical shell, and the space in between was filled with aluminum oxide fragments to the purpose of thermally insulating the channel and prevent ing intense conveotion of the stagnant external water. Fig. 5 shows a close-up view of the exit section of the channel.
The entire assembly was inserted in a test section housing designed to withstand the pressure.
The housing was made of a 4" schedule 80 stainless steel pipe connecting two terminal stainless steel heads maohined to provide flanged electrically insulated passages for the electrical connectors.
The manufacturing difficulties of the channel and the limited size of the controlled atmosphere furnace, reduced the available heated length of the test section to 590 mm.
Water flow was measured by a turbine flow meter as well as an orifice plate, the former allowing recording of the water flow signals.
Two sheat type thermocouples were used for water inlet temperature measurements, whereas five thermocouple of the same type were located at different positions of the exit flow area enabling an evaluation of the water temperature tranverse distribution.
Fig. 6 indicate the relevant dimensions of the ohannel flow area and the positions of the five thermocouples locat ed at the channel exit.
3. Control of the subchannels geometrical symmetry
The tests preliminary performed and referred to in a previous paper /!ƒ, were considered as a check on the over all feasibility of the mixing experiments in the designed test apparatus.
In fact,in the course of the above runs, a primary tran sverse geometrical asymmetry was discovered in the two adjacent channels through the check of some distributions of the exit water temperatures over the flow area obtained from experiments
9 -
with symmetric heat generation. This primary asimmetry could be charged to several geo
metrical imperfections observed in the earlier prototypes of the channel.
The improvement of the manufacturing technique of the channel and the use of a second set of ceramic spacers, allowed to achieve the symmetry requirements for the complex flow passage in cold conditions. As a check of the overall reliability of the experimental set up in hot condi tions, tests were made aiming at the control of channel symmetry with the fluid circulating at the operating pressure and temperature.
In these check runs the water exit temperature distribu tion was assumed as experimental evidence of the transverse symmetry of the system.
The following check tests were performed:
- steady-state tests with heating limited alternatively to the two rods.
steady-state tests with simultaneous symmetric heat gene ration limited to the two rods.
steady-state test with heating limited to the channel walls only.
Figs. 7 and 8 show the results obtained for 3 typical check runs giving for each detection point of the exit flow area the ratio θ of the local to the average ooolant temperature rise.
These plots show the existence of a fairly good degree of symmetry in the channel.
- 10
4. Burnout experiments
4.1. Range of parameters
The following range of parameters was covered in the present experiments: - Mass flow rate: 49 - 230 gr/cm sec - Pressure : 52-139 ata - Inlet temperature: 190 - 329°C.
As for the heat flux ratios, namely the burnout heater heat flux to other heaters heat flux ratio, several values were tested ranging from 0 to 1.
4.2. Burn-out data presentation
Burn-out data have been reported in Tables I through V and plotted in Fig. 9 through 13. The symbols Φ_ Q , Φ. and Φ„ appearing in these representation indicate respectively:
Φ_, _ = burnout heat flux of the "burnout rod" u.U. Φ. = heat flux of the "adjacent rod" Φ3 = heat flux of the "shell".
The power is generated in the shell both in the curved sections as well as in the flat thin strips.
The last term contributes only for 15$ of the total shell power.
11 -
As for the shell heat flux Φ3, their values have been computed accounting only for the power and the surface of curved section of the duct.
In Fig. 9 through 13 burnout heat flux values are report ed as a function of the coolant inlet temperature for the different heating conditions tested.
5. Remarks
Fig. 12 shows how, for the same inlet conditions, the heat flux on the burnout rod decreases with increasing the power generated on the shell.
Examination of the Figg. 9 through 11 suggests that, for equal inlet conditions of the coolant, the burnout heat flux on the so called "burnout rod" is unaffected by the degree of heating of the adjacent rod.
The same conclusion may be drawn from the results represented in Fig. 13.
This result could be explained assuming that a mutual oom pensation sets in along the channel between the effects of flow redistribution and thermal mixing.
However, the independency of the critical power on the B.O. rod with respect to the conditions in the adjacent channel, has been verified on such a large variety of coolant flow rate and enthalpy conditions, that it seems unlikely that redistribution and mixing effects might have balanced through out the tests. It is more reasonable to admit that, on short heating lengths, as the one tested in our experiments, the mixing and redistribution effects do not have any relevant
12
influence on the behaviour of at least a portion of the coolant cell associated to the burnout rod.
On the other hand, some experimental B.O. data of preliminary tests conducted with the test section here described, showed that the burnout heat flux on the "burnout rod" was to a certain extent affected by the degree of heating of the "adjacent rod". The trend observed was a small decrease of the burnout heat flux on the B.O. rod with increasing the heat flux of the adjacent rod.
However, in the course of the systematic experiments, whose results are here reported, this effect was never confirmed so that the preliminary data were considered rather related to some imperfections present in the first assembly.
Therefore, before drawing any conclusion on the results here reported, it is worth to obtain additional experimental evidences about the effect of transverse transport of fluid upon the critical heat flux. This work should be carried out in a different test channel, having the same lattice parameters as the one described in this report, in order to be able to find out whether the trend suggested by the data here presented is affected or not by the particular structure of the tested channel.
It is anticipated to perform experiments with transverse distribution of heat generation in a 9 rod bundle test section next to be tested in the SORIN pressurized water loop.
- 13
Acknowledgements
Appreciation is expressed for the constant coopération of Mr. Morocutti of the Euratom.
The fruitful discussions with Mr. Previti of the FIAT Atomio Power Department are gratefully acknowledged.
Thanks are also due to the Metallurgy and Ceramios Laboratory of the FIAT APD for having made the task of brazing the various parts of the flow channel.
The authors are indebted to Mr. Sonavero, Mr. Fumerò, Mr. Mina-zio, Mr. Passavanti and other members of the SORIN Heat Transfer Laboratory for the fine work performed throughout the present experimental program.
Finally the help offered by the SORIN workshop in manufacturing the test seotion is acknowledged.
14
Bibliography
¿Vf F. Biancone, A. Campanile, G. Galimi, M. Goffi, "Forced convection burnout and hydrodynamic i n s t a b i l i t y experiments for water a t high p re s su re . Pa r t I : Presen t a t i on of data for round tubes with uniform and nonuniform power d i s t r i b u t i o n " , Report EUR 2490.e, 1965.
¿2/ A. Campanile, G. Galimi, M. Goffi, " Inves t iga t ion of burn out hea t f lux in a double adjacent and communicating channels t e s t sec t ion with t ransverse ly varying heat genera t ion" , Contr ibut ion to the Round Table of the European Two-Phase Flow Group - Section 4 . 1 . - C.C.R. I s p r a , 1 4 - 1 7 June 1966.
TABLE I
Burn-out dataiheating on burnout rod only.
Run
18(21-2-67)
58(26-7-67)
74(7-12-66)
120(26-7-67)
56(9-12-66)
64(21-2-67)
74(18-1-67)
20(19-7-67)
22(19-7-67)
45(7-12-66)
69(24-7-67)
106(26-7-67)
49(9-12-66)
Pressure a t a
132
132
130
132
131
133
132
132
132
130
134
132
132.5
Flow IA
880
855
943
1030
1020
2650
2640
2670
2670
2700
2800
3060
3195
Mass flow r a t e
gr/cm2sec
51.6
50.1
52.2
53.9
51.9
154.6
152.4
154.2
152.3
147.9
153.5
155.7
160.9
I n l e t subcooling
«»C
93.7
92.7
60.3
38.0
27.6
91.1
84.2
83.7
76.7
55.8
57.9
28.2
25.6
I n l e t temperature
oc
236.7
237.7
269
292.5
302.3
240
246.2
246.7
253.7
273.5
273.7
302.2
305.3
Power kW
49.6
47.4
43.1
33.8
34.0
71.2
63.0
66.4
64.4
58.2
57.9
47.2
44.3
Φ B.O. Watt/om2
262.3
250.7
228.0
178.8
179.8
376.6
333.2
351.2
340.6
307.8
301.5
249.6
234.3
Ul I
Follows Table
Run
54(18-1-67)
45(26-7-67)
50(21-2-67)
90(7-12-67)
01(26-7-67)
6(21-2-67)
20(9-12-66)
I .
Pressure a ta
133
132
131.5
132
132
132
132
Flow 1/h
3180
3880
3800
3875
4325
4400
4670
Mass flow r a t e
gr/cm^sec
155.8
228.1
219.6
214.4
219.8
221.9
230.0
I n l e t subcooling
°C
18.1
94.2
84.9
61.3
27.8
26.0
18.7
I n l e t temperature
°C
313.0
236.2
245.2
269.2
302.6
304.5
311.8
Power kW
41 .0
84.1
83
71.2
53.5
50.8
48.7
Φ B.O. 2
Watt/cm
216.9
444.8
439.0
376.6
283.0
268.7
257.6
TABLE I I
Run
22(21-7-67)
48(21-7-67)
58(24-7-67)
40(21-7-67)
58(21-7-67)
17(26-7-67)
30(26-7-67)
44(24-7-67)
40(26-7-67)
16(24-7-67)
81(21-7-67)
89(21-7-67)
23(24-7-67)
Pressure a t a
134
135
134
134
136
133
133
134
131
132
133
136
130
Flow
iA
870
900
2800
3910
4010
850
2610
2830
3890
340
950
1015
2640
Burn-out datacheat ing
Mass flow r a t e
gr/cm2sec
50.6
50.3
151.7
221.4
221.4
50.0
151.2
154.5
227.7
49.4
53.1
53.3
152.4
I n l e t subcooling
°C
88 .6
85.7
52.3
73.8
62.3
95.1
85.8
56.1
91.1
95.0
66.3
41.5
82.3
on both r o d s .
I n l e t temperature
°C
243
264.5
279.3
257.8
270.5
236.0
245.2
275.5
238.7
235.5
264.7
291.2
247.0
Total power
kW
73.4
66.5
94.2
119.4
111.2
84.1
122.9
107.8
153
92.3
80.1
66.2
130.3
B.O. rod power
kW
46
41.9
57.3
74.8
69.3
46.3
67.1
59.2
82.8
47.1
40.8
33.9
66.7
Φ B.O.
Watt/cm2
243.3
221.6
303.1
395.6
366.5
244.9
354.9
313.1
437.9
249.1
215.8
179.3
352.8
ΦΑ Φ
B.O
0.595
0.587
0.644
0.596
0.604
0.816
0.832
0.821
0.848
0.959
0.963
0.953
0.953
■vi
I
Follows Table II.
Run
48(20-7-67)
62(20-7-67)
74(20-7-67)
35(24-7-67)
67(21-7-67)
96 (21-7 -67)
P r e s s u r e a t a
134
134
134.5
131
134
132
Flow 1/h
2640
2930
3350
3840
3980
4430
Mass flow r a t e
gr /cm sec
150.1
160.5
163.8
224 .6
217.3
221.3
I n l e t subcoo l i ng
°C
75 .9
57 .6
17 .7
90 o 6
56.1
22 .5
I n l e t t e m p e r a t u r e
°C
255.7
274 .0
314.2
239.2
275.5
308.0
T o t a l power
kW
127.4
117.2
8 3 . 5
168.0
132.0
100 .6
B.O. r o d power
kW
64 .6
59 .3
4 2 . 6
85 .1
65.8
51
Φ B.O. 2
Watt/cm
341.7
313 .6
225 .3
450.1
348 .0
269.7
Φ A
Φ B.O
0.972
0 .976
0 .960
0 .974
1 .006
0 .972
00 I
TABLE I I I
Burn-out da ta :hea t ing on the B.O, rod and on the s h e l l .
Run
53 (3 -7 -67 )
5 ( 3 - 7 - 6 7 )
6 (3 -7 -67)
35 (3 -7 -67 )
50 (3 -7 -67 )
47(13-7-67)
58(13-7-67)
16(13-7-67)
40(13-7-67)
32(13-7-67)
P r e s s u r e a t a
130
132
132
134.5
135.5
133
132
134
132
134
Flow 1/h
2435
2440
2630
3010
2980
2330
2535
2570
2770
2980
Mass flow r a t e
g r / cm 2 sec
139.6
138.0
145.5
151.0
135.5
135.0
141.0
140 .6
138.8
136.4
I n l e t s u b c o o l i n g
°C
7 8 . 3
72 .0
60.9
24 .9
16 .7
86 .1
64.0
57.1
23 .5
2 .45
I n l e t t e m p e r a t u r e
°C
251.0
258 .4
269 .6
307 .0
315.8
245 .0
266 .5
274.5
307 .0
329 .2
T o t a l power
kW
119.9
112.2
112.3
8 5 . 0
7 3 . 3
161 .6
143.8
134.7
110.0
8 8 . 0
B.O. rod power
kW
57 .4
53 .5
5 2 . 6
40 .3
34 .7
55 .3
49 .3
47.1
38 .0
30 .2
Φ B.O. Watt/cm
303.6
283.0
278.2
213.1
183.5
292 .5
260 .7
249.1
201.0
159.7
φ 3 ΦΒ.Ο
0.445
0 .452
0 .480
0 .460
0 .450
0 .835
0 .830
0.831
0.838
0.848
TABLE IV
Burn-out da ta :hea t ing on both rods and on the s h e l l .
Run
10(19-1-67)
24(19-1-67)
37(19-1-67)
47(19-1-67)
40(17-1-67)
91(17_1_67)
117(17-1-67)
50(14-7-67)
74(14-7-67)
88 (14-7 -67)
95(14-7-67)
P r e s s u r e a t a
133.5
134.5
136
135
129.5
134.5
134
133
135
134
141
Flow iA
2600
2744
2975
3316
2750
3036
3210
2370
2460
2750
2770
Mass flow r a t e
g r / c m 2 s e c
148.6
150.7
156.4
158 .6
153 .6
156.0
155.0
135". 5
132.7
140.4
137.0
I n l e t s u b c o o l i n g
°C
79.1
59 .9
42 .3
12.7
64.9
33 .2
14 .6
7 8 . 3
51 .5
30.1
23 .9
I n l e t t e m p e r a t u r e
°C
252.2
272.0
290.5
319.5
263 .7
298.7
317 .0
252 .7
280 .7
301 .5
311 .7
T o t a l power
kW
133.8
121 .1
113.1
8 7 . 6
149
122.3
97.1
198.1
168.4
149.2
135.9
B.O. r o d power
kW
55 .5
50 .2
46 .9
35 .9
5 1 . 6
42 .5
34 .2
51 .0
4 3 . 7
38 .9
35 .2
Φ B.O. 2
Watt/cm
293 .5
265 .5
248.1
189.9
272 .9
224.8
180.9
269.7
231.1
205 .7
186.2
ΦΑ
*B.O
0 .434
0 .436
0 .437
0 .465
0.581
0 .579
0 .567
0 .890
0 .883
0 .872
0 .872
Φ3
Φ ΦΒ.Ο
0.419
0 .415
0 .412
0 .407
0 .555
0.541
0 .539
0 .856
0 .820
0 .819
0 .823
Ο
Follows Table IV.
Run
13(19-7-67)
47(18-1-67)
22(18-1-67
38(18-1-67)
Pressure a t a
130
132
135
139
Flow
iA
2630
2952
3100
3180
Mass flow r a t e
gr/cm sec
151.0
156.0
160.9
154.2
I n l e t subcooling
°C
81 .3
42.2
37.1
18
I n l e t temperature
°C
248.0
288.3
295.1
316.5
Tota l power
kW
212.7
167.0
158.6
130.9
B.O. rod power
kW
54.9
43.9
41.7
34.4
Φ B.O.
Watt/cm
290.4
232.2
220.5
181.9
ΦΑ Φ
B.O
0.903
0.863
0.868
0.869
-îiL Φ
B.O
0.852
0.823
0.815
0.808
ι
ro
TABLE Y
Burn-out data hea t ing on both r o d s .
Run
7(20-7-67)
18(20-7-67)
30(20-7-67)
74(2-8-67)
1
Pressure a t a
52.5
53
55
53
Flow iA
1775
1785
1890
1975
Mass flow r a t e
gr/cm2sec
110.7
106.4
107.7
110.7
I n l e t subcooling
°C
75.7
44.3
20.0
9.6
I n l e t temperature
°C
190.0
222.0
248.7
256.7
Tota l power
kW
158.6
134.2
113.4
74.6
B.O. rod power
kW
79.3
68.2
57.6
39
Φ ΦΒ.Ο. Watt/cm2
419.4
360.7
304.6
206.3
ΦΑ Φ B.O
1
0.968
0.969
0.913
ro
23
ofr «noi
"1
Alf·,
.//tfft
J HtíTt»
c nounou
©-
2 0 KW
n C H C / O E R
i l i -f i t Pi
ORMt .
1χ=" ' L O W =»=·
M S WAID
ncssuucR
r^ 90 TU
U I coax»
«m OPCRATCO reto PUMP
2 0 KW P R O C M E R
ál ΟΟι
ICSI
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m π-ι
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DISC
TS
BT
PASS
(.HtttO MOTOR fs^jj f
CITY
WATFR
£ £ £ f
i RCLicr
VAIVI
BLOWDOWN LWC
ΤΟ Α Τ Η
® PRESSURE
© TEMPERATURE
Fig . 1 - Flow diagram.
- 24 -
SORIN SALUGGIA
SEZIONE DI PROVA N°4 CONTORNO DEL CANALE RISCALDATO.
SCALA CS '/
DIS. ^gp
DATA
/9f4 N.· SOM 9?i
Fig. 2 - Cross section of flow passage.
Fig. 3 — Close-up view of the channel showing the location of the spacers.
- 26
+ shunt
B.O. Rod
R
Adjacent Rod
Shell
R2 4-
Fig . 4 - Schematic diagram of the e l e c t r i c a l connection arrangement.
— 27 —
Fig. 5 — Close-up view of the exit section of the channel.
28
a = 1,5 mm
b = 2,9 mm
Fig. 6 - Relevant dimensions of the flow passage showing the positions of the exit water temperature probes.
29
Q O Û;
ó CD
Ζ
o
o Ζ t—
< UI X
Q O
UJ O < —> Q <
Ζ O
o
<
X
θ
?
1
η
o
o
< >
<>
o
0—L L o - o - 0J ·—0*—
Inlet, temp. 210 °C
Pressure 120 ata
Flow rate 5000 l/h
Total power 30 KW
Temperature probe positions
θ
,0„ΓΛ. . -ÍQ-Q — Ql 1— Q
Temperature probe positions
Vig. 7 - Transverse coolant temperaturs rise for several points of
the exit section during tests for control of the subchannels
geometrical symmetryι Asymmetrical heating.
30 -
Inlet temperature Pressure Flow rate
Total power
202 °C 110 ata 2875 l /h
627 KW
θ
Ui Q
O ca
o ζ
t— < LU Χ J^\J^S.
Ο-Ο-θ
Temperature probe positions
Fig. 8 - Transverse coolant temperature rise for several points of the exit section during terts for control of the subchannels geometrical symmetryt Symmetrica"', heating.
31
«00
300
200
100
S
δ χ
,Δ # D
BURN OUT HEAT FLUX
IN EXPERIMENTS WITH
UNHEATEO SHELL.
NOMINAL MASS FLOW RATE
50 gr/cnrfsec
NOMINAL PRESSURE
132 a t ·
SYMBOL Φ./ Φ a»
Δ 0 □ 059
V 081
O 0,96
δ
(Δ
INLET TEMPERATURE °C
200 250 300 350
Fig. 9 - Burnout heat flux in experiments with unheated
shell. ρ
Nominal mass flow rate 50 gr/cm sec
Nominal pressure 132 ata
32
400
300
200
100
o
χ
_| b.
S ζ
^
BURN OUT HEAT FLUX
IN EXPERIMENTS WITH
UNHEATEO SHELL.
NOMINAL MASS FLOW RATE
156 gr/cntsec
NOMINAL PRESSURE
132 ata
SYMBOL Μι« Δ 0
α 059
V 081
O 0,96
¿D
INLE
Λ
0
Γ TEMPERAT URE e
C
200 250 300 350
Fig. 10 - Burnout heat flux in experiments with unheated
shell. «
Nominal mass flow rate 156 gr/cm sec
Nominal pressure 132 ata
- 33
500
400
300
200
100
0
iE
χ
!
I
Δ° ν
BURN OUT HEAT FLUX
IN EXPERIMENTS WITH
UNHEATEO SHELL.
NOMMAL MASS FLOW RATE
225 gr/crrfsec
NOMINAL PRESSURE
132 ata
SYMBOL ♦./φ» Δ 0 α oss V 081
O 096
D
α
( J
INU
Δ
O
:r TEMPERATI JRE »C
200 250 300 350
Pig. 11 - Burnout heat flux in experiments with unheated
shell. 2
Nominal mass flow rate 225 gr/cm sec
Nominal pressure 132 ata
34
400
300
200
100
iE Ü.
»
X
_l b.
X
Δ
O
BURN OUT HEAT FLUX
IN EXPERIMENTS WITH
HEATED SHELL.
NOMINAL MASS FLOW RATE
156 gr/cm e«c
NOMINAL PRESSURE
132 ata
SYMBOL M.. i /Φι«
Δ 0 0
D 0,U3 0,413
V 0576 0,545
O Q876 0824
Δ
D _ £
ν π
t
α ο
ο*
Δ
D <9
INLET TEMPERATURE °C
200 250 300 350
Fig. 12 - Burnout heat flux in experiments with heated shell,
Nominal mass flow rate 156 gr/cm2sec
Nominal pressure 132 ata
35
400
300
200
100
"fe „o
X
3 b.
UI χ
e
BURN OUT HEAT FLUX
IN EXPERIMENTS WITH
HEATEO SHELL AND
AOJACENT ROD AL
TERNATIVELY HEATED
OR UNHEATED.
NOMNAL MASS FLOW RATE
137 gr/crrvstc
NOMINAL PRESSURE
132 ata
SYMBOL ♦r/i. Φ, /i« O 0 083
O 088 0,83
o e
4 >
o
INLE1
°e o
' TEMPERATU 1
•
RE »C
200 250 300 350
Fig. 13 - Burnout heat flux in experiments with heated shell
and adjacent rod alternatively heated or unheated.
Nominal mass flow rate 137 gr/cm2sec
Nominal pressure 132 ata
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