2383
.pdfcomposite structure with a 4 mm thickness of the steel pipe wall allowed for corrosion. The diameter of a pile is 813 mm and thickness is 16 mm. Reinforcing bars are placed in the uppersection of the piles.
The cross section of the deck is a traditional composite structure of two open girders. The girders are 3.2 m high I- beams (Fig. 33). There are crossbeams at 7 m centres. On the crossbeams there is a 1 m high secondary longitudinal girder. In the north part of the bridge, where the deck is 30 A wide, there are two secondary girders.
The cable crossbeams are inclined to the cable direction. Between the main girders, the cross section of the cable crossbeam is an open I-beam. The girders are stiffened with steel bars. Outside the main girders, the cable crossbeam is a composite box girder.
In the competition proposal, the pylon was a steel structure. In the general design, the costs of steel, composite and concrete pylon were compared. The concrete pylon proved to be the most economical.
The pylon is formed of two T-shaped hollow concrete towers which are joined together by two crossbeams. There is an elevator inside one tower and stairs inside the other. The horizontal geometry of the road has a curvature of R = 4000 m. This caused large horizontal forces on the towers. Therefore, the pylon was not placed centrally to the deck cross section, but with an eccentricity of 0.6 m. Due to this placement, the horizontal forces, and hence, the number of steel piles decreased considerably.
The bridge has 24 factory-fabricated parallel wire cables. The cables consist of 7 mm steel wires (253-403/cable) injected with grease inside a high density polyethylene pipe that is covered with white Tedlar tape. The pylon and cables are illuminated at night.
The fixed bearing of the bridge is at the southern abutment. It is a hinged structure, where horizontal forces are transferred large steel bars.
CONSTRUCTION
The piling and the concreting of the foundation slabs and columns took 14 months. The joint welding of the steel girder sections and the launching were completed in one year. The largest concrete works, such as towers and deck slabs, were placed in summer, because the temperature in winter can be as low as -25 °C.
At the beginning of the construction period, the design for the pile foundation was changed to a caisson structure. The caissons were built in a dammed trough on the north side of the bridge. The caissons were floated into position and the piling work was done through access holes in the caisson slab. Finally, the piles and the inner part of the caisson were cast in dry conditions. Except for the slab of supports T3 and T9, all casting work on the substructure was done in dry conditions. The casting of pile slabs succeeded well and there were no faults typical of underwater concrete casting.
The steel girders of the superstructure were launched from both abutments
and joined by welding between supports T5 and T6. Three auxiliary piers had to be built for the cable:stayed spans during launching. The top of the girder was lifted on a pontoon when the spans exceeded 70 m. The launching bearings were vertically adjustable because the girder was very stiff. The longest beam sections were 42 m long and the maximum weight was almost 80 t.
The bridge was originally designed using steel grade Fe 355 E, but the steel contractor and steel manufacturer proposed to change the steel grade of the support sections of the girder to a new thermomechanically manufactured S 420 ML steel. Using this material, the contractor slightly reduced the weight of the girder and benefited from the superior welding properties of the new steel grade. The total amount of steel in the superstructure is about 50501.
The towers of the pylon were cast using a climbing formwork, with the height of one casting section being 4.15 m. The longitudinal reinforcing bars were jointed with screw sleeves.
The crossbeams between the towers and the cable anchor areas were pre: stressed. The surface of the concrete tower had to meet stringent quality requirements. A textile covering was placed on the formwork surface to enhance the strength of the concrete surface and to reduce air blisters. A green concrete paint was applied to the surface of the pylon.
Construction of the pylon was complicated because it has three inclined walls. Therefore, the scaffolding had to be adjusted at every stage. The
reinforcing of the cable anchor area was difficult because of restricted space. The temporary support structure of the upper crossbeam was also difficult to install and there were problems to stabilise it. Nevertheless, the pylon was completed on schedule and all casting work was completed before winter.
The deck slab of the superstructure was cast using two movable scaffolding units. The longest casting section was 24 m. The slab was prestressed transversely in two equal stages.
The stay cables were installed from the bottom upwards. Cable stressing was accomplished using four jacks at the level of the deck slab. The cables were stressed in pairs. The total weight of stay cables is 214 t. They were tested against fatigue and ultimate load, the test cable being the largest cable of the bridge. In the fatigue test, where a 5 m long test Cable was loaded 2 million times with a stress variation of 193 MPa, only 9 wires broke. After this test the same cable was stressed up to the breaking load, 24.6 MN.
Client:
Mikkeli Road District
Design:
Suunnittelukortes AEK Ltd, with Leonhardt, Andra and Partner
Main contractor: WT Corporation Ltd
Steel contractor: PPTH Steel Ltd
Construction duration: January 1991 to November 1993
The Pitan Bridge, Taiwan
Kwong M. Cheng |
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constraints and concerns that guided |
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Pres., |
OPAC Consulting |
Engineers, |
the design of the bridge, it had to: |
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San Francisco, CA, USA |
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- meet all freeway design and perfor- |
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Introduction |
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mance requirements of the Northern |
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Taiwan Second Freeway |
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be |
aesthetically |
pleasing, |
To alleviate traffic congestion near |
constructable, and economical |
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Taipei, in 1985 the Taiwan Area Na- |
- require minimum maintenance. |
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tional Freeway Bureau planned the |
The following factors were considered |
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construction of the 108 km long North- |
in the selection of the bridge type: |
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ern Taiwan Second Freeway. The ma- |
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Structural systems issues such as |
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jority of the Second Freeway's align- |
bridge piers, span lengths and |
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ments are on grade, on embankments, |
arrangement, foundations, vertical and |
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in tunnels, or on viaduct structures. At |
horizontal clearances, capacity to resist |
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several |
locations, |
however, |
obstacles |
horizontal forces and seismic actions, |
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were identified that required special |
etc. |
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bridges. The Pitan Bridge spans one of |
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Aesthetic issues such as the overall |
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these areas. |
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appearance of the bridge, its com- |
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The Pitan Bridge, actually two nearly |
patibility with the surrounding land- |
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parallel bridge structures, is located |
scape and with existing built facilities |
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about 15 km south of Taipei. It |
- Construction issues such as the con- |
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connects typical low-level viaducts to |
struction method, equipment, con- |
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a tunnel. Both bridge units have a total |
struction time and the capabilities of |
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length of approximately 800 m, a 750 |
local contractors |
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m radius curvature and a slope of |
- Cost issues such as the cost of relat- |
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approximately 1%. The Pitan Bridge |
ed |
works, |
of maintenance |
and the |
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has become a landmark in this subur- |
cost of the bridge itself. |
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ban area of Taipei. |
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Four bridge types consisting of varia- |
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SELECTION OF THE BRIDGE |
tions on girder-and-arch designs were |
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identified as potentially meeting the |
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TYPE |
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above design considerations. |
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The selected bridge type consists of a |
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The design of the Pitan Bridge was |
post-tensioned cast-in-place concrete |
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based primarily on the 1983 AASHTO |
box girder bridge deck supported on |
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Standard Specification for |
Highway |
delta-shaped reinforced concrete box |
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Bridges, the 1987 AASHTO Design - |
piers, which are joined together at the |
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and Construction |
Specifications for |
centre of the main span to form an |
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Segmental Bridges (No. 2 Draft), and |
arch. This scheme adapts well to the |
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local design codes. Among the general |
constraints of the site and provides a |
stiff, strong bridge with a clean, effi- |
structural layouts. They each consist of |
cient, and very modern appearance. |
nine spans totalling 781.5 m, with a |
BASIC LAYOUT |
160 m main span. The northbound |
bridge has an additional simple span of |
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21.7 m (Fig. 35). |
The two almost parallel bridge structures have nearly identical
Fig. 35
Expansion joints have been kept to a |
The preliminary design made use of |
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minimum, located only at the extreme |
simple and rational analytical tools that |
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ends of the structure. The four main |
have proven reliable for many |
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bridge piers (3, 4, 5 and 6) are fixed to |
structures. The following were consid- |
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the girder and footings with monolith- |
ered at this stage of the design in order |
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ic, moment-resisting connections. The |
to determine the dimensions of the |
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smaller piers and the abutment are |
main structural elements of the bridge: |
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fixed to their footings only and support |
the cross section, the longitudinal sys- |
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the girder through bearings that are |
tem, the pier shafts, footings and piles. |
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fixed |
transversely, |
having |
some |
SUPERSTRUCTURE DESIGN |
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limited freedom-to slide longitudinally. |
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This combination of few expansion |
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joints and high pier fixity was evaluat- |
Detailed design and analysis made use |
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ed for serviceability under the required |
of more refined analytical tools in or- |
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seismic excitation, as well under the |
der to verify the preliminary design. |
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influence of creep and shrinkage in the |
The following tasks were performed: |
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concrete, and temperature change in |
- development of structural models for |
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the |
structure. |
The |
piers |
and |
service-load analysis |
foundations provide enough flexibility |
- evaluation of design values for mo- |
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so that the time-dependent strains and |
ment and shear |
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temperature strains of the concrete, |
- transverse and three-dimensional |
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accumulated over the entire girder |
considerations |
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length between expansion joints, cause |
- pier moments, shears, and axial |
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acceptably small bending stresses in |
forces |
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the piers and axial stresses in the gird- |
- thermal effects. |
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er. |
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The bridge superstructure consists of a |
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single cell box girder (Fig. 36). The di- |
mensions of the box girder were de- |
The web longitudinal prestressing is |
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signed to comply with the strength re- |
dimensioned to provide adequate mo- |
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quirement as well as provide space to |
ment capacity and stress control at |
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house the necessary prestressing ducts. |
mid-span and over the pier to resist su- |
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The main span girder depth varies |
perimposed dead load, live load, creep, |
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from 8.882 m at the face of the delta- |
and temperature moments. Each of |
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shaped pier to 3.5 m at mid-span, and |
these tendons extends over the full |
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is prestressed longitudinally with can- |
length of a span, and is anchored in the |
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tilever tendons in the top slab and con- |
diaphragm walls over the pier. |
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tinuity tendons in the webs. All pre- |
The deck transverse prestressing is di- |
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stressing is grouted in ducts embedded |
mensioned to resist transverse bending |
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in the slabs and webs of the girder. |
from dead load and live load. The gird- |
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er cross-section reinforcement includes |
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a grid of mild steel bars in each direc- |
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tion on each face of each structural el- |
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ement. |
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The delta-shaped piers are designed to |
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reduce the length of the main span, |
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thus allowing the relatively slender |
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box girder to meet the strength and |
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stiffness demands on this bridge. They |
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are designed as wall-type elements |
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with post-tensioning to provide a |
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Fig. 36 |
residual compressive stress |
under |
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The top deck longitudinal prestressing |
combined axial force and bending for |
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is dimensioned to resist all structural |
all service load conditions. The |
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dead loads during cantilevering, as |
schematic prestressing layout of the |
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well as construction loads and the |
main span is shown in Fig. 37. |
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weight of the travelling formwork. All |
SEISMIC |
ANALYSIS |
AND |
anchorages are located in the well- |
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confined and reinforced intersection |
DESIGN |
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fillets at the tops of the webs. |
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Fig. 37
Initial, seismic analyses were perseismic design criteria. These analyses formed in accordance with the local provided controlling conditions for de-
sign of the piers and foundations. |
and no plastic hinges develop below |
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A more refined analysis using earth- |
the ground surface. |
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quake response spectrum developed |
Foundations consist of 2.0 m diameter |
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for the vicinity of the site, was used |
drilled, cast-in-place, reinforced con- |
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later to verify structural dimensions |
crete piles, supporting reinforced con- |
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and reinforcement requirements. |
crete footing blocks. The piles, up to |
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Substructure Design |
14 m in length, act as friction piles |
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with some limited end-bearing support. |
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Each pier consists of a four-walled cel- |
Analysis and Modelling |
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lular reinforced concrete shaft, heavily |
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reinforced to form a ductile cellular el- |
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ement. All fixed piers participate in |
Constructability will largely determine |
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providing the required capacity to re- |
the success of a project. Therefore, a |
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sist seismic and horizontal forces. For |
thirty-eight step stage-by-stage analy- |
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transverse seismic loads, the piers be- |
sis of the bridge was performed to vali- |
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have as cantilevers, with significant |
date the time-dependent behaviour of |
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moments developed at the bottom |
the construction sequence. The analy- |
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only. For resisting longitudinal seismic |
sis included: |
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excitation, the main piers behave as |
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development of structural computer |
members in a rigid frame. The creep, |
models for construction procedure |
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shrinkage, and temperature deforma- |
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evaluation of stresses and deflections |
tions of the superstructure are ade- |
at critical construction stages |
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quately accommodated in the mono- |
- evaluation of stresses and deflections |
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lithic piers by the flexibility of the |
over the service life of the bridge. |
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foundations and the pier shafts. |
The bridge was modelled using a com- |
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The basic cross section of the main |
mercially available general-purpose |
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piers continues through the depth of |
structural analysis program which is |
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the box girder cross section to provide |
capable of static and dynamic analysis |
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diaphragms capable of developing the |
of finite element models for a wide |
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plastic moment of the pier into the |
range of structure types. |
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girder. These diaphragms also provide |
All important structural features of the |
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a convenient location for anchorage of |
bridge were modelled, including the |
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the longitudinal prestressing tendons in |
piers, the box girder, and the delta- |
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the superstructure. |
shaped piers. The girder was modelled |
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The abutment is designed as a conven- |
as a line of frame elements represent- |
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tional cantilever wall which supports |
ing the entire cross section, oriented |
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the bridge girder on sliding bearings. |
along the centroidal axis of the proto- |
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The footing blocks supporting the piers |
type girder. The piers were modelled |
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were designed for the static dead and |
similarly, including semi-rigid ele- |
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live impact loads and the seismic loads |
ments in the pier-girder intersection. |
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such that the movements at the base of |
The intersection zone between the |
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the piers are within allowable limits |
delta-shaped piers and the girder was |
modelled by a separate finite element |
distribution between the diaphragms |
model in order to capture the stress |
and the webs in this area. |
ROOSEVELT LAKE BRIDGE, GILA COUNTY, ARIZONA |
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Maurice D. Miller, Civil Eng. |
portant, the deciding factor for the new |
HTNB Corp., Kansas City, MO |
Roosevelt Lake Bridge was flood |
Crossing Roosevelt Lake |
protection. When the US Bureau of |
Reclamation raised the dam by 23.5 m |
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to provide additional protection to |
Located in Gila County, a rugged area |
Phoenix and the Valley of the Sun, it |
of east-central Arizona, Roosevelt |
removed State Highway 188 from the |
Lake is a hydroelectric reservoir used |
dam. |
for flood control, irrigation and recre- |
Bridge Type Selection |
ation. It is midway between the cities |
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of Globe, which is the county seat, and |
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Payson, in a ranching and recreational |
Located about 305 m upstream of the |
area. State Highways 88 and 188 con- |
dam, the new Roosevelt Lake Bridge is |
nect the two major cities. From Globe, |
just below the confluence of the Salt |
Route 88 winds northwest through |
River and Tonto Creek. Here, the Salt |
desert canyons and along the south- |
River just begins the erosion of its |
west shore of Roosevelt Lake to a ma- |
canyon through the Mazatzal Moun- |
sonry dam, where it connects with |
tains. The steep-walled features of the |
Route 188 and continues west and |
canyon were ideal for the construction |
north to Payson. |
of the world's highest masonry dam, |
The one-lane road traversing the dam |
creating a lake 300 m wide and 60 m |
across Roosevelt Lake had not been |
deep at the proposed crossing. |
improved since construction of the - |
The Arizona Department of Trans- |
dam in 1911. Travel across the dam |
portation based its selection of the best |
was slow and treacherous, with abrupt |
type of bridge for the crossing on eco- |
90° blind corners. When two cars met |
nomics. Because of the steep valley |
on the dam, one had to yield the right- |
walls and the deep valley floor, under- |
of-way and back up, a gesture that was |
water foundations were determined to |
not always made willingly by the local |
be too costly. The two-lane bridge |
ranchers. |
would have to span the lake with foot- |
Because of the narrow and crooked |
ings on each shore. Two engineering |
route over the dam, vehicles over 9 m |
firms prepared complete construction |
in length were prohibited. Commercial |
plans for two alternatives: a steel box- |
traffic between Globe and Payson was |
rib-through-arch and a concrete stayed |
forced to detour through Phoenix, |
girder bridge. |
adding hundreds of miles to the route. |
The box-rib-through-arch was selected |
Although traffic congestion was im- |
for the steel alternative based on an in- |
depth study of three steel bridge types: |
box section varies from 2.44 m at the |
trussed-through-arch, box-rib-through- |
crown, where compressive forces are |
arch, and cable-stayed girder. The |
the smallest, to 4.27 m at the base, |
twisting alignment required for the |
where compressive forces are the |
mountainous terrain made it difficult to |
greatest. The shape of the arch rib was |
get a tangent alignment long enough to |
also established to minimize the dead |
accommodate minimum-length back |
load bending stress in the arch. The re- |
spans for the cable-stayed and trussed |
sultant shape is defined by both second |
arch bridges. |
order and fourth order curves, making |
The arch span was the most economi- |
the entire arch appear smooth and |
cal. It adapted readily to the curved |
continuous. |
alignment of the approach structures |
The steel arch rib section is made up of |
and had superior aerodynamic proper- |
two 1.2 m-wide flanges with two web |
ties. The welded steel arch was the |
plates that vary from 2.44 m at the |
overwhelming favorite of most |
crown to 4.27 m at the base plate. The |
bidders. It was bid at 30% less than the |
webs of the box section are stiffened |
concrete alternative. |
by two T-sections welded to each web. |
Arch Rib Design |
The stiffeners are continuous and par- |
ticipate fully in carrying the various |
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loads. Sixteen longitudinal fillet welds, |
Existing terrain and future lake levels |
over 13.4 m long, were required to |
were important factors in establishing |
connect the flanges and the stiffeners |
the arch rib geometry. The arch spring- |
to the webs. |
line is at Elevation 649.5 m, well |
Stability against global buckling and |
below the 200-year flood elevation of |
transmission of wind loads for the arch |
663 m. To keep the steel arch above |
rib, which is 15.2 m center-to-center, |
water, the lower 158 m of the arch rib |
was achieved through the use of a K- |
is made of concrete. The resulting |
bracing system fabricated from struc- |
composite steel-concrete structure |
tural tubing and welded box sections. |
consists of the following sections: 21.6 |
The selection of the K-bracing was |
m of concrete rib, 323 m of steel rib, |
based on both first-cost and life cycle |
and 21.6 m of concrete rib, for a total |
costs. The K-bracing required 901 less |
arch rib length of 366.4 m and an arch |
steel and reduced wind deflections to |
span of 329 m. |
half as much as those caused by a |
The steel and concrete portions were |
comparable Vierendeel system. The |
made continuous by anchoring a base |
closed tubular sections were selected |
plate at each of the steel-concrete con- |
to minimized corrosion due to |
nections. This required 32 MN of pre- |
entrapment of water and debris. To to- |
stress force at each base plate. |
tally close the ends of the tubular |
The geometry of the entire arch rib op- |
shapes, horseshoe-shaped plates were |
timizes the use of material through the |
welded to the ends of the tubes. |
length of the rib. The depth of the steel |
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At the portals, the K-bracing was terminated with a three-dimensional X- shaped connection. The multi-jointed, three-dimensional intersection of the bracing was achieved by welding plates into an octagon and welding the ends of the tubes to the sides of the octagon. More than 760 m of fillet welds were used to make up the bracing.
Another part of the bracing system is a 2.1 m square welded box strut between arch ribs directly below the roadway at each end of the bridge. Access to the interior of the ribs is through lockable doors in these boxes. Electrical distribution centers are also inside the struts. The floor system for the 11.5 m wide roadway consists of longitudinal stringers, supported on welded I-girder floor beams. Floor beams are spaced at 15.2 m centers and are hung from the arch ribs with eight wire ropes, four at each end of a floor beam. Welded steel girders 2.0 m deep are used as exterior stringers and also function as stiffening girders for aerodynamic ''stability. About 2.1 m of fillet welds were required to fabricate the floor system. The overall stiffness of the system - arch ribs, bracing, and floor - was verified by wind tunnel tests.
Erection of the bridge was accomplished
using temporary towers resting on the arch footings and a system of bridge strand
backstays and forestays. Hydraulic jacks in
the stays allowed alignment adjustments to be
made during erection.
The erection progressed by lifting and bolting successive 15.2 m long welded steel rib sections into place with a barge-mounted crane floating on the lake. As adjacent rib sections were placed, the welded tubular K-bracing was installed to maintain alignment and rigidity of the ribs. Shop fabrication accuracy was maintained so well that there were no mismatches during erection.
Owner:
Arizona Dept of Transportation
Engineers:
HNTB Corp., Kansas City, MO
Main contractor:
Edward Kraemer & Sons, Inc., Plain, WI
Service date: 1990
ERECTION
BRIDGE SCOUR FAILURES |
Introduction |
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D.V. Mallick M.M.Tawil |
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Technical Advisors |
Failure of a bridge is viewed seriously |
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National Consulting Bureau, Tripoli, |
by the public since it involves not only |
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Libya |
traffic disruption and the loss of tax |
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payer's money but can also result in |