4.2 - VSL
4.2 - VSL
4.2 - VSL
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For complicated structural systems, the<br />
determining mechanisms have to be found.<br />
Descriptions of such mechanisms are<br />
available in the relevant literature, e.g. [31],<br />
[36].<br />
In special cases with irregular plan shape,<br />
recesses etc., simple equilibrium considerations<br />
(static method) very often prove to be a<br />
suitable procedure. This leads in the simplest<br />
case to the carrying of the load by means of<br />
beams (beam method). The moment<br />
distribution according to the theory of elasticity<br />
may also be calculated with the help of<br />
computer programmes and internal stress<br />
states may be superimposed upon these<br />
moments. The design has then to be done<br />
according to Method A.<br />
3.12. Ultimate stength of a<br />
cross-section<br />
For given dimensions and concrete qualities,<br />
the ultimate strength of a cross-section is<br />
dependent upon the following variables:<br />
- Ordinary reinforcement<br />
- Prestressing steel, bonded or unbonded<br />
- Membrane effect<br />
The membrane effect is usually neglected<br />
when determining the ultimate strength. In<br />
many cases this simplification constitutes a<br />
considerable safety reserve [8], [10].<br />
The ultimate strength due to ordinary<br />
reinforcement and bonded post-tensioning<br />
can be calculated on the assumption,<br />
which in slabs is almost always valid, that<br />
the steel yields, This is usually true also for<br />
cross-sections over intermediate columns,<br />
where the tendons are highly concentrated.<br />
In bonded post- tensioning, the prestressing<br />
force in cracks is transferred to the concrete<br />
by bond stresses on either side of the crack .<br />
Around the column mainly radial cracks open<br />
and a tangentially acting concrete<br />
compressive zone is formed. Thus the<br />
so-called effective width is considerably<br />
increased [27]. In unbonded post-tensioning,<br />
the prestressing force is transferred to the<br />
concrete by the end anchorages and, by<br />
approximation, is therefore uniformly<br />
distributed over the entire width at the<br />
columns.<br />
Figure 27: Tendon extension without lateral restraint Figure 28: Tendon extension with rigid lateral restraint<br />
8<br />
Figure 26: ultimate strenght of a<br />
cross-section (plastic moment)<br />
For unbonded post-tensioning steel, the<br />
question of the steel stress that acts in the<br />
ultimate limit state arises. If this steel stress is<br />
known (see Chapter 3.1.3.), the ultimate<br />
strength of a cross-section (plastic moment)<br />
can be determined in the usual way (Fig. 26):<br />
m u =z s . (d s - xc ) + z p . (d p - xc) (3.9)<br />
2 2<br />
where<br />
z S= A S . fsy (3.10.)<br />
z p = A p .(σ p∞ + ∆σ p ) (3.11.)<br />
x c =<br />
zs + zp (3.12.)<br />
b . f cd<br />
3.1.3. Stress increase in unbonded<br />
post-tensioned steel<br />
Hitherto, the stress increase in the unbonded<br />
post-tensioned steel has either been<br />
neglected [34] or introduced as a constant<br />
value [37] or as a function of the<br />
reinforcement content and the concrete<br />
compressive strength [38].<br />
A differentiated investigation [10] shows that<br />
this increase in stress is dependent both upon<br />
the geometry and upon the deformation of the<br />
entire system. There is a substantial<br />
difference depending upon whether a slab is<br />
laterally restrained or not. In a slab system,<br />
the internal spans may be regarded as slabs<br />
with lateral restraint, while the edge spans in<br />
the direction perpendicular to the free edge or<br />
the cantilever, and also the corner spans are<br />
regarded as slabs without lateral restraint.<br />
In recent publications [14], [15], [16], the<br />
stress increase in the unbonded post-<br />
tensioned steel at a nominal failure state is<br />
estimated and is incorporated into the<br />
calculation together with the effective stress<br />
present (after losses due to friction, shrinkage,<br />
creep and relaxation). The nominal failure<br />
state is established from a limit deflection au .<br />
With this deflection, the extensions of the<br />
prestressed tendons in a span can be<br />
determined from geometrical considerations.<br />
Where no lateral restraint is present (edge<br />
spans in the direction perpendicular to the free<br />
edge or the cantilever, and corner spans) the<br />
relationship between tendon extension and<br />
the span I is given by:<br />
∆I<br />
= 4 . au . yp =3 . au . dp (3.13.)<br />
I I I I I<br />
whereby a triangular deflection diagram and<br />
an internal lever arm of yp = 0.75 • d, is<br />
assumed The tendon extension may easily<br />
be determined from Fig. 27.<br />
For a rigid lateral restraint (internal spans) the<br />
relationship for the tendon extension can be<br />
calculated approximately as<br />
∆I<br />
=2 .( au . ) 2 +4 . au . hp I I I I<br />
(3.14.)<br />
Fig. 28 enables the graphic evaluation of<br />
equation (3.14.), for the deviation of which we<br />
refer to [10]<br />
The stress increase is obtained from the<br />
actual stress-strain diagram for the steel and<br />
from the elongation of the tendon ∆I<br />
uniformly distributed over the free length L of<br />
the tendon between the anchorages. In the<br />
elastic range and with a modulus of elasticity<br />
E p for the prestressing steel, the increase in<br />
steel stress is found to be<br />
∆σ p = ∆I . I . E p = ∆I . E p (3.15)<br />
I L L<br />
The steel stress, plus the stress increase ∆σ p<br />
must, of course, not exceed the yeld strength<br />
of the steel.<br />
In the ultimate load calculation, care must be<br />
taken to ensure that the stress increase is<br />
established from the determining mechanism.<br />
This is illustaced diagrammatically