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CHAPTER 5: MECHANICAL PROPERTIES
5.1
(i) Constant stressing rate
Therefore
Differentiating
Therefore
dO" = R = constant dt
I dO" Maxwell model' Equation (5.44) (page 324): de dt
- --
de dt
R
e Rt
+ -11
since 0" = J R dt
de Voigt model, Equation (5.52) (page327): dt
+
d2e 1 dO" E de ----dt 11 dt 11 dt
Ede 11 dt
R = 0 11
. R dO" SInce =-dt
Edt
0"
0" + -
Ee
11
11
This is a differential equation which can be solved in one of several ways. One is the
'convolution integral' method outlined by J.G. Williams in Stress Analysis of Polymers. The
simplest method is to 'guess' the result as follows:
Therefore
where T = !J.. o E
R. J. Young et al., Introduction to Polymers© Springer-Verlag US 1992
52
and
The equation then becomes
- ~ 1 + E R [1 -exp [ - ~ 1 ] ~ ~ E ~
Cancelling throughout the relation between e and t becomes
R - - = ° T]
Hence it has been shown that the solution that was guessed is correct.
(ii) Constant strain rate
de = S = constant dt
Maxwell model, Equation (5.44) (page 324):
Therefore
or d<1 (S~ - (1)
Integrating gives
In (S~ - (1) = Et + A ~
where A is the constant of integration.
Since when t = 0, <1 = ° then A = In (ST])
de dt
= Edt ~
1 <1 +
Edt
R
~
Hence
Therefore
53
Et
11
where To = !!.. E
Rearranging gives
Therefore
5.2
a 10-+-----,
Voigt model: de dt
(J Ee = S 11
(J = Ee + S11
(J = ESt + S11 . S e SInce =-t
o;-------~------------------------------e -----
o~------~--------~---------o 100 200 tis
(a) t=100s Thus 1(100 sj = 10 [1 - exp [ - ~~ ~]J
Therefore J(100 s) = 2(1 - e-O.5) = 0.787 m2 GN-1
But
e J=(J
therefore e = J (J
Therefore e(100 s) = 0.01 GN m-2 x 0.787 m2 GN-1 = 0.00787
54
(b) If stress was not removed the strain after 200 s would have been
e(200 s) = 0.01 GN m-2 X 2 m2 GN-1 X (1 - e-1) = 0.01264
The removal of stress is equivalent to the addition of a negative strain of
0.00787 after (2oo-1oo)s.
Therefore residual strain = 0.01264 - 0.00787
Strain after 200 s = 0.00477
5.3
The Maxwell model for stress relaxation is given by Equation (5.49) (page 326) as
Therefore
Therefore
5.4
Therefore
In one cycle
CTO = strain X short-term modulus
CTO = 0.2 x 3 MN m-2 = 0.6 MN m-2
Leaking pressure = 0.3 MNm-2 = 0.6 MNm-2 exp [ - t 1 300 days
t = 208 days
e = eo sin wt
CT = CTo sin (wt + 0)
CT = CTo sin wt cos 0 + CTo cos wt sin 0
flU = J CT de
21rlw
flU = f CT de dt t dt
55
But de dt = eow cos wt
Therefore
2",/",
!::..U = ! eow coswt (0"0 sinwt coso + 0"0 coswt sino) dt
2",/",
= eowO"o ! (coso sinwt coswt + sino cos2wt) dt
Therefore
5.5
co co co
Evaluate f f f -00-00-00 (1)
Given that
co
f exp( - (32X2) x 2dx = 11"112/2{33 -co
(2)
and
co f exp( - (32X2) dx = 11"112/ {3 (3)
-co
Multiplying out the first term within the integral (1) gives
56
00 00 00
J J J ~5 [O .. ~ - 1)x2 exp( _/32X2) exp( -/32y2) exp( _/32Z2) + ...••..•..•••••• ] dxdydz -0)-00-00
Integrating w.r.t. x using (2) gives for the term inside the square brackets
[ (Ai - 1) 1r1l2 exp( -/32y2) exp( _/32Z2) + ••••.....••...•...•••..••.• J 2/33
Integrating w.r.t. y using (3) gives
[ 2 1r1l2 1r1l2 2 2 J (Al - 1) 2/33 73 exp( -/3 z) + .••••••••••••••••••.•••••••••
Integrating w.r.t. z using (3) gives
[0,; - 1) 2~ ";" + ....................•.. J
Performing the same exercise for all terms leads to the integral becoming
5.6
w = II2G(AI2 + A22 + A/ - 3)
For two dimensional straining, volume is constant
Therefore Al A2A3 = 1
and so Al = A2 = A, A3 = lIA2
therefore w = jG [2),,' + :. - 3]
Hence
a'
57
The forces per unit area in the unstrained state are It, h and h in each direction.
Then the work done by these forces will be in general:
dw = ItdAl + hdA2 + hdA3
But It = h = f and h = 0
Therefore
and so
These forces are related to the true stresses i.e. the forces on the strained area O'h 0'2 and 0'3 by
Therefore
where O't is the two-dimensional true stress.
Therefore
or
5.7
0' or f = .-!.
A
The stress-strain curve for the polymer is given by
0' = aeb I (1)
58
where (Jt = true stress, e = nominal strain and a and b are constants.
The Considere construction for a neck to form is given by Equation (5.153) (page 359) as
---(1+e)
Hence, from (1)
d(Jt b 1 = abe -
de
Also from (1)
(1 +e) (1 +e)
Hence, for necking
ae b ---
(1+e)
Cancelling gives
b 1 e (1 +e)
or e = b/(1 - b)
Yield will occur when, putting (5) into (1)
5.8
(2)
(3)
(4)
(5)
The pressure-dependent von Mises yield criterion is given by Equation (5.161) (page 364)
Let the tensile yield stress = (Jyt and the compressive yield stress = Uyc
Therefore the criterion can be written as
59
ACTy, + 2BCT;, = 1 (tension)
-ACTyc + 2BCT~ = 1 (compression)
Therefore
Hence the criterion becomes
Let the critical hydrostatic pressure to cause yielding be Pc, then Equation (5.2)(page 312) gives
Pc = %(CT1 + CT2 + CT3)
and CTl = CT2 = CT3
The criterion becomes
Therefore
5.9
Plane stress deformation CT3 = 0
Yield criterion, Equation (5.161) (page 364): A[CTI + CT2] + B[(CTI - CT2)2 + CT22 + CT12] = 1
Craze criterion, Equation (5.170) (page 370): CT1 - UCT2 = X + YI(CTI + CT2)
From 5.8
But
Therefore
and
and B = 1I(2CTycCTy,)
(J = 92 MN m-2 and (J = 73 MN m-2 yc yt
A = 2.829 X 10-3 m2 MN-1
B = 7.445 X 10-5 m4 MN-2
60
Crazing: 0"1 = 47 MN m-2, 0"2 = 0
and 0"1 = 45 MN m-2, 0"2 = 45 MN m-2
Therefore
47 MN m-2 = X + Y/47 MN m-2
45 MN m-2 - (0.33 x 45 MN m-2) = X + Y/(45 +45) MN m-2
Therefore
x = 11.73 MN m-2
Y = 1657.6 MW m-4
Therefore the two equations become
Shear yielding:
Crazing:
Crazing and shear yielding will take place simultaneously at values of 0"1 and 0"2 which satisfy
both of the above equations. They can be solved by plotting the two functions graphically.
Crazing \
-100 -60
, , , ,
100
-60
-100
, , , ,
-2 m
61
This gives U1 = 59 MN m-2 and U2 = - 30 MN m-2
and U1 = - 30 MN m-2 and U2 = 59 MN m-2
The curve for crazing has not been plotted on the opposite side of the U1 = -U2 line, since
crazing can only take place when the overall hydrostatic stress is tensile.
5.10
The chain direction repeat in polyethylene is 2.54 A
Therefore
Therefore
u/MN m-2
0
40
80
120
100
200
dOO2 = 1.270 A (un strained)
The modulus E = stress/strain = u/e
Strain, e = tJ.d/d but A = 2d sin ()
d = A/(2 sin ()
()/degrees d/A
37.483 1.26700
37.477 1.26717
37.471 1.26734
37.466 1.26749
37.460 1.26766
37.454 1.26783
tJ.d/A tJ.d/d
0 0
0.00017 0.000134
0.00034 0.000268
0.00049 0.000387
0.00066 0.000521
0.00083 0.000655
Therefore the modulus - 300 GN m-2
5.11
This problem is taken from:
Bevis, M. (1978), Coll. Polym. Sci. , 256, 234 and
Young, R.I. et ai, (1979) J.Poiym.Sci: Poiym. Phys. Ed. , 17, 1325.
General sketch of twins in plane of shear:
u/e MN m-2
298507
298507
310077
307101
305343
(hk2»
62
The (hkO) planes bend by an angle of 24>
across the twin boundary.
(a) If the planes of molecules that bend or kink are of the type (hkO) the twinning plane is
(hk2) and hence:
Plane of molecules
(200)
(020)
(110)
Twinning Plane
(202)
(022)
(112)
(b) The angle is 24> and from the sketch it can be seen that:
tan 4> = cl2dhkO (c = 2.537 A)
The values of dhkO can be calculated from the crystal geometry as shown in Question 4.1
(hkO) d,dA tan 4> 24> (hk2)
200 3.700 0.343 37.8° 202
020 2.465 0.515 54.5° 022
110 4.103 0.309 34.4° 112
(c) The direction of shear lies in the twinning plane, (hk2) and in the plane of shear.
(hkO) (hk2) Plane of Shear Direction of Shear
200 202 (010) [202]
020 022 (010) [022]
110 112 Irrational -[112]
The plane of shear and direction of shear are irrational for the (112) twin.
63
(d) The magnitude of the shear, s, is given by
s = 2 tancf>
Therefore the twin with the lowest shear is the (112) twin.
5.12
(1f = 85 MN m-2
Kc = 1.25 MN m-3/2
~ 25mm
a
The sheet contains 'inherent flaws' equivalent to small cracks of length, ll{). The equation for
Kc in Table 5.5 (page 404) for a single-edge notched specimen can therefore be used.
i.e. L 112
K = _a_ [1.99 - 0.41(alb) + 18.7(alb? - 38.48(alb)3 + 53.85(alb)4] c bt
As the flaws are very small a ~ b
Therefore
112 Kc - Lj ao x (1.99Ibt)
where Lj is the fracture load
Therefore
or
112 -1 ao = (1j x (Kj1.99)
Hence
64
a~12 = 1.25 MN m-3/2/(85 MN m-2 x 1.99)
or
ao = 55 x 10-6 m = 55 J.'m
5.13
The data show Uf decreases with increasing crack length, a.
It should be assumed that the width of the polystyrene specimen is very much greater than the
crack length, hence equations (5.193) and (5. 195)(page 401) can be used
[ ]
112
EGc (J = -f 7f'a
(1)
(2)
Hence it is necessary to plot uf versus a- Ifz to first determine Gc
(JclMPa almm a-'hlm-1f,
17.2 10 10.00
17.5 9 10.54
17.9 8 11.18
18.4 7 11.95
19.0 6 12.91
20.0 5 14.14
22.0 4 15.81
25.0 3 18.25
31.0 2 22.36
40.0 1 31.12
41.0 0.5 44.72
42.0 0.1 100.0
50
40
co 30 0.. ~
'" -b 20
10
65
-- -o---------------~
o 10 20 30 40 50 60 70 80 90 100
a-1/2/m-1I2
It is possible to fit a straight line to the initial data points. The final 3 points fallon a different
(dashed) line.
The slope of the initial line is 1.117 ± 0.03 MPa mlh
a) Hence from (1)
[ E~, 1 In • slope. 1.117 MPa mIn
Therefore with E = 3 GPa
G = 7r X 1.1172 MPa2 m c 3 x 1()3 MPa
Gc = 1.307 X 10-3 MPa m
G = 1 307 J m-2 c
66
b) From (2)
Kc = 1.98 MN m-312
c) The inherent flaw size, ao can be determined from the change in slope of the lines on the
graph (ie at a-'h = 33 m-1h)
5.14
For the elastomer sheet
Hence ao = 1 mm.
S = KaW
and da = qsn = q(Ka wy dt
If a sheet is held at constant extension
1 dt = ---
x da
The crack grows from ao to a where a approaches the sheet width in time t.t,
then
Therefore
But n is generally large and a ~ ao
67
Hence, the equation for t.t approximates to
t - 1 f - 1
qKlIWll(n - 1)a;-