Report
S5i298
FIRST
RESULTS OF WDDE
PG 86-29
PLATE TESTING
UNDER
FATI:GUE LOADING AT
LOW
TEMPERATURE
Deift, 1986
TUD 'ft
Department of Marine Engineering-
ei
Ship Structure laboratoryTechnical University DeIf t
ir. H.G. Schoite
ir. E.vanRletbergeh
CONTENTS INTRODUCTION SPECIMEN 2
2.1 Materi1
2 2.2 Geometry and instrumentation2 TEST PAOCEDURE
3 DISCUSSION OF THE RESULTS
4
4.1Meagurement data
44.2 Failure assesment evaluation
4
Nomenclature a - c:racklength mm ac - critical cracklength mm ap - prefatigue cracIc.length mm An - net-section area B thickness mm
CTOD - crack tip opening displacement mm
Fa - reserve factor on cracklength
FK - reserv.e factor of fracture toughness
FL - load factor
K - stress intensit;y factor
MPam
Kc - critical stress intensity factor MPa'lm
Kr - maasure of proximity to LEFM failure
Lr - measure of proximity to plastic yielding,
Pf - fractùre ìoad MN
Pum
- limit load MNPnet - load at yielding in net-section MN
Pt:ol - tolarable load MÑ
Temp - test temperature degree.s C
W - haïf width of wide plate mm
Ey
-
yield straIna - overall stress MPa
of - flòw stress (ay+outs)/2 MPa
o.net - net-section stress MPa
aûts - ultimate tensile strength MPa
ay - yield strength MPa
- d'imensíònless ClOD
1. INTRODUCTION
Testing. wide plates under fatigue load òondition.s at low
temperature is a continuation of the small scale fatigue bending
tests at low temperature (fabalt-test) in the NIL, fracture
programme 1 1) . The wide plate experiments are carried out to
verify if the results .òf the small scale. tests are applicable, to
components of more complexity. For this purpose two wide plates
are to be tested in the Sh:ip Structure Laboratory (SSL) of the
De.l'ft University of Technology. This report prese'nts the first
resulte of the first wide plate that was tested.
The experiment on the first Wide. . plate has not been completed
yet. In consequence. of. some considerable time delay due to
building-in and rapairing problems, the experiments are stopped
for the time ben.g on behalf of other tests of higher priority.
The experiments will 'be continued as soon as possible.
After present1ng the test data a:nd a short discussion of the
results, the first fracture result.will als.o be evaluated Using
2 'SPECIMEN
2.. 1 Material
The wide plate was made of a Fe 51ONb steel which is the same
steel that was usad in the small scale. fabalt-tests.
The welding procedure of. the three welds in the wide plate is
also similar to that of the small scalé tests. For further
details see [1] and [2].
2. 2 Geometry and ins'trurnen:tation
The specimen was composed of
four
welded plates as shown infig.1. This means that three welds can be tested under the same
load conditio'ns. Each weld was provided with a mechanical notöh
with a geometry shown in fig.2. Likethe smal.l scale specimens
the notch was also situated in the center of the weld and can be
consideradas a flat through the thickness defect.
The instrumentation of the plate consisted of strain gauges on
three plate sections and three weld sGctions, and COD spring
gauges ovez the notch. The position
of
the strain gau;ges and CODspriñg gauges is shown in fig.3.. Strain gauges nr. 1-6 were
placed to record the s.tPess distribution of the plate. The other
strain gau:ges, in line with the notch, weré placed to give an
indication
of
the amount of crackgrowthduring fatigua at lowtemperature. The temperature was controléd by 7 thermocouples.
The COD spring gauges were placed to indicate the amount of
deformation at the cracktip (fig.4).
3. TEST PROCEDURE
The wide plate was tested in the 6 MN fatigue machine of the SGL.
The e:xperiment started with precracicing the defects
in the three
welds. The amount of fatigue precracking and other
test
conditions, are listed in table 1.
After precracking, the specimen was insulated and cooled to the
test temperatura by a nitrogen cooling device at the canter of
the plate and a sup:p.orting alcohol òooling device for both the.
side welds. The temperature for the center weld was selected at
-80
oc. This temperature was chosen to verify fracturing duringfatigue w.hich occured in the, small scale fabalt-tests. After
cooling the center weld, the side welds appeared to have a
temperature o-P -60 °C. This temperatura was adapted as test
temperature for the side welds.
The plate. was tasted at a frequency of 2 Hz and with a strass
ratio-of R=0.1. The test was performed by applying a.constant
maximum fatigue. load of 4.403 MN. Adjusting the. fatigue load to
maintain a constant stress sïtuation at the cracictip was. not
applied because of the absence of a reliable cracklength
measuring method. This way o-P testing results in a critical
region where fracture is most likely to occur. Hodever, compared
to small scale specimen this region. is considerably larger, and
is estimated as 30-40 mm for the present wide plate.
The plates were welded in the test-rigs in as welded condition.
To avoid introducing secundary stresses the plates were not
stretched; Unfortunately the deflection from the load line
appeared to be larger as expected, and therefore high banding
stresses ware introduced during fatigue testing.. Because strain
gauges were placed at both sides of the plate, the bending effect
could be quantified and will be taken into account in the
4. DISCUSSION OF THE RESULTS 4.1 Measurement data
In fig..5 the strain gauge measurements ore plotted as a function
oP the number of cycles for the variuo.s sections. As can be
concluded from fig.S high bending stresses of the some magnitude
as the axial tension stress have occured in the center of the
plate. The bending effect at the side welds is considerably less.
The sudden change in strain gauge measurement data le caused by
fracture in one 0f the connecting welds. Because of repairing
this weld and placing of additional brackets the stress
distribution appeared to. have changed. The stress distribution
over the wide plate can be il.lustrate.d by fig.6 at three
different moments during this experiment.
Fig.? shows the COD values as a function of the number of cycles.
The cracktip value was not calculated because no reliable
calculatiOn method was available for this geometry. Hcwev'er, the
COD-values indicate fracture at low toùghness values which
correspond to the resultsof the small scale tests.
The geometry of the fracture surface, shown in fig.8, illustrates
the great influence of the bending effect. The fracture surface
was examined and a fracture initiation point was located as
indicated in fig.6. The position df this point w.illbe used for
calculating the critical c.racklength.
4.2 Failure assasment evaluation
The moment 0f fracture of the center weld and the current
situation et the side welds hove been evaluated us;ing two failüra assessment methods, the COD design cùrve (3]. with the revision of
Dawe:s [4), and the' R6 Rev.3 method (5]. For this purpose the
critical c:r'acklength was calculated 'from the Initiation point on
the fracture surfoàe. The applied stress was evaluated taking.
into account the bending effect derived from the strain gauge
measurement data. '
Table 2 and fig.9 presents the relevant data and calculation
results for the COO design curve method. For
thecritical
ClOD-value use was made of the average ClOD-value at that temperature
(indicated as av.) and of the minimum ClOD-value (min.). As can
be seen the moment of fracture on the certer of the weld would
'hove been predicted safely using this methòd. in contrast With
the results of the stati,c wide plates in [6], fracture would not
have been predicted safely when yielding in the net-section would
have been used as a criterium. Comparing critical and actual
cracklength of both side welds, fracture at one of thOse welds
was 'very unlikely to occur and would have meant a very bad
result.
The relevant test doto and calculation results foi- the CEOB R6
Rev.3 method are gathered in table 3 and illustrated in fig.1O.
The, results 0f this calculation show similar results as the COD
design curve. Fracture a.t the center weld is predicted safely and
fracture occuring at the side welds Was very onlikely. The
results are however less conservative compared to those from the COD design curve.
LITERATURE
Schalte, H.G., Rietbergen, E1 van,"Fatigue
bending-tests at
low temperature on welded specimens of 30mm and
70mm
thickness", Ship Structure Laboratory Report No. 302,
Deift 1986.
Koning,, C.,".NIL-breuktaajhejdsonderzoek/Nederlöflds
program-ma. Uitnameplan en type pPoefstuIcken", TNO-rep;ort.
85M/35/08862/KoÑ[p,EV BRE 84-11, 2 juli 1954 (in Dutch).
British Standards Institution, "Guidance on some method.s for
the acceptance levels for defects in fUsion welded joints",
PD 6493, B.S.I. 1980.
Dawes, M.G.,"The ClOD design curve approach: limitQtlons,
finite size and application."; The Welding I:nstitute,
July 1985.
Mime, I.
et al ,"Assessment o-F the i.ntégrity of structurecontaining defects", Central Electricit.y Generating Board,
R/H/R6-Revision 3, May 1986.
[6) Rangen, H.J.M. van,."Prediction of tolarabÏe loads, for 17
wide plate tests in the NIL-fract:u.e.program, üsing the
design curve (ClOD) approach.", TNOreport BSM/O11959/RON
/SCN, BRE 85-25, 26 september 1985.
Tb1e I.
Te5t partioulor.Weld test prefatlgue
crack1enth
ai-ca netto load attemp. cracklength at fracture area fracture
ap a 28W An
Pf
Oc mm mm mm2 mm2 MN
Li -60 17.3 34.8 20014 18884 4.403
L2 -80 19.8 92.3 20160 14660 4.403
Table 2. CTOD design curve1 Weld Temp 28w Li L2 L3 weld Li L2 L3 oc mm2 mm2 average ClOD
O/ay
a MPowith last revision of' Daweà :
n( 1-a/W)
Pf aret a Pnet PÇ/Pn CTOO ClOD
ay*An av. min.
MN MPa MPa MN mm mm p2.3 35 minimum CTOD o/ay Weld a Temp MPA °C matérial prôperties ay o-F' outs Ey
MPA MPa MPa %
266 -60 592 639 686 0.276.6 83 -80 620 666 711 0.2884 --60 22196 19690 -80 20150 14560 -60 21328 1892Ó 4.403 224 1.98 . 11 68 0.38 0.246 0.160 4.403 302 219 9.03 0.49 0.070 0.043 4.403 232 206 11.20 0.39 0.246 0.160 0.359 0.609 361 0.233 0.483 0.029 0.170 105 0.018 0.134 0.359 0.609
Table 3. Failure assesment method CEGB R6 - Revision 3.
Weld Temp. Pf B W a Kc ay Pnet Lr a K Kr
MN mm mm mm MPa[m MPa MN MPa MPaifm
Li -60 4.403 36.8 310 35 178.1 592 11.68 0.377 223 74.4 0.418
L2 -80 4.403 32.5 310 92.3 101.1 620 9.03 0.488 285.2 161.8 1.60
L3 -60 4.403 34.4 310 35 178 592 11.20 0.394 233 77.8 0.447
Limit condition Reserve factors
Weld Lr K Plim a FK FL Fa
MN mm
Li 0.488 0.961 5.70: 97.5 0.43 0.77 0.36
L2 0.305 0.987 2.75 38.6 1.62 1.60 2.39
connecting weLd
notched X-wetds fo be tested.
4 Strain gages (.0.0. clip-gage Theèmö couple 3/4 P4C 3/4 7a 9 11/12 1410 lOa -/T218 T54 2
qig.3., Instrumertat.iOflQf tche wide plate.
I Irontside/bachside F /1147 (thermo couplel T3/-,A-/C.1 11/12 '7:C2/(3 (c:oo.-bridgesl
T
C.0.-bridge. (.1 C. 3 /C.2 sf'ig.4. Detail 0f COD spring gauge Instrumentation Inst rume n ta t ion
D'l 3/6 ,/ Fitt4i C2/ 410 t1Oa -/12 +5/6 A-A 8-B
p_ IO 2U000 L.1 L.1 30000 i..GOi.IiciOw_7 :1 j200
1.001
P.2 30000n 6442 P3 L.1 P.1 1.2 P.2 1.3 n =15851 P.3 Li P.1 12 P2 13 e Froottide of plate Backtide of pille P3 1.1 Pl 1.2 P.2 13 n= 22894
.fig.6. Stress distribution over the wide plate at three
different stages during, the experiment. Numbers refer to eE/1000 RN values.
-=1
____I-I
451JflB
'76'Ç\is
1hk
3S.511 68.8 i-..-..
18.'_.j111255 -1wJ - -111fr'65 i )l1,I fu9696 I /P'30,3I
l3bj
:-H
. 1=1
I=1
. I I'/
85.7 775 _________ 101.7."'.ti'
,1Il6 1'" huìis7.3
01.7 aSS I. eU,\
401. . 36.3 6611 b 76,3- II
253 9353 JIll Jjfr69 727 _.11hiT . 47.6 74.7 68.7-
43.2 . 0117.8 JjJQ6--
86.7i
.137
Zz.z . 1 3=1
2a4 J17;:L
=
L,
. 70.6 90.2 '5 , , -9l 544 .-
179.2 __7.2 -.---. . 435 .7
I
¡ nat fracture n 92 o:i Section 1.2. + (.2 .c.1 + + + 100 20000 n + + + s .30000 0,1- 0,00- 0.06- 0,04-0,02 o Section L.1 +s
++
++
.
mm .c.Q0 + C.2 (.1 s n 30h00 mm ato 0.10- 0.08- 006- 0.04- 0.02-Section 1.3*
'e 'efig.7 COD measurements
welded se9tl.ons. t + C2 o (.1
t
o 000 20000 30.000fatigue notch sawcut notch
+HInhiuim C.T.OEO. Hean C.T.O.ft
Unsafe Area
C.T.O.D. design curve
0.0101 I I
1.0 10,0
fig.9.
COD design cUrv
diagram.
Safe Area
0.2 0,6 0.6 0,8 1,0 1,2
Lt