7/28/2019 13-3- Modelling of Fsw
1/36
7/28/2019 13-3- Modelling of Fsw
2/36
Author & year Title Source
C. Chen & R.
Kovacevic
(2004)
Thermomechanical modelling and force
analysis of friction stir welding by the finite
element method
J. Mechanical
Engineering Science,
218 : pp 509-519
7/28/2019 13-3- Modelling of Fsw
3/36
AIM
A 3D finite element method is proposed to study the thermal
history and stress distribution in the weld and subsequently, to
compute mechanical forces in the longitudinal, lateral and vertical
directions.
7/28/2019 13-3- Modelling of Fsw
4/36
Model Description
Tool Material -AISI A2 steel
Shoulder diameter -24 mm
Pin Diameter -6 mm Base material - Al 6061-T6
Workpiece dimensions
200 mm 50 mm 6.4 mm
7/28/2019 13-3- Modelling of Fsw
5/36
Material properties of tool and
workpiece material
7/28/2019 13-3- Modelling of Fsw
6/36
Heat transfer model
The rate of heat generation derived from the friction for a
single element at the interface is
dq= 2 (T) p(T) dr
is the rotational speed of the tool
(T) is the coefficient of friction between the tool and the materialp(T) is the pressure on the shoulder of the tool
The rate of heat generation over the entire interface
of the contact will be
q=2/3 ( (T) p(T) (Ro3-ro3))
Where Ro and ro outer radii of the tool and the probe respectively
7/28/2019 13-3- Modelling of Fsw
7/36
Mechanical model
Displacement is given by
U= [D] where [D] is the displacement function matrix
In the displacement formulation, the essential
boundary conditions are specified as
Uy =0
The stressstrain equation is described as
S= [M]
7/28/2019 13-3- Modelling of Fsw
8/36
7/28/2019 13-3- Modelling of Fsw
9/36
Meshed model
7/28/2019 13-3- Modelling of Fsw
10/36
Experimental setup
7/28/2019 13-3- Modelling of Fsw
11/36
Three axis force measurement device
7/28/2019 13-3- Modelling of Fsw
12/36
Results and Discussion
7/28/2019 13-3- Modelling of Fsw
13/36
Study of thermal history
A comparison of the calculated and the measured temperature histories at the
location 10mm to the weld centre-line and 1.6mm below the top surface of the plate
V =140mm/min and = 500 r/min)
7/28/2019 13-3- Modelling of Fsw
14/36
A comparison of predicted temperature distribution and measurement along the
lateral direction for nodes 1.6mm below the top surface of the plate (V = 140 mm/min,
= 500 r/min and t =34 s)
7/28/2019 13-3- Modelling of Fsw
15/36
Analysis of stress distribution
Predicted principal stress
distributions in the welded plate
and the tool in three directions at a
time of 34 s (step 20) after the start
of welding: (a) x direction; (b) y
direction; (c) z direction
7/28/2019 13-3- Modelling of Fsw
16/36
Parametric study of three axis force component
Analysis of effects of rotational speed on force components
7/28/2019 13-3- Modelling of Fsw
17/36
Predicted mechanical force histories in three directions at various rotational
speeds of the tool: (a) 344 r/min; (b) 500 r/min; (c) 757 r/min (under constant V
=140 mm/min)
7/28/2019 13-3- Modelling of Fsw
18/36
Analysis of effect of traverse speed on force
components
Predicted mechanical forces in three directions at various traverse
speeds of the tool =500 r/min
7/28/2019 13-3- Modelling of Fsw
19/36
Comparison of predicted and measured mechanical force histories in threedirections
CONCLUSIONS
7/28/2019 13-3- Modelling of Fsw
20/36
CONCLUSIONS
The stress data are subsequently used to predict the three axial force
component.
Parametric studies have been carried out to determine the effect of the
rotational speed, the traverse speed on the stress distribution, and the
mechanical force.
The prediction shows that the longitudinal force is strongly influenced by the
welding parameters.
It decreases with increase in the tool rotational speed and increases with
increasing traverse speed. A strong fluctuation in force occurs in thelongitudinal direction.
The vertical force decreases with increase in the rotational speed and
increases slightly with increase in the traverse speed
7/28/2019 13-3- Modelling of Fsw
21/36
Conclusion Contd..
The lateral force has a weak link with the
rotational speed and increases slightly with
increase in the traverse speed
7/28/2019 13-3- Modelling of Fsw
22/36
Discussion
7/28/2019 13-3- Modelling of Fsw
23/36
Author & year Title Source
Nandan et al.,
(2007)
Improving reliability of heat transfer and
materials flow calculations during friction stir
welding of dissimilar aluminum alloys
Welding journal, 86 :
pp 313-322
7/28/2019 13-3- Modelling of Fsw
24/36
AIM
Friction, slip between the tool and the workpiece, heat
transfer at the bottom surface, and internal heat generation
were studied for their effects on model reliability
Optimization of uncertain parameters
Prediction of temperature fields and magnesium
concentration profiles were examined
7/28/2019 13-3- Modelling of Fsw
25/36
Process Parameters
h l d l
7/28/2019 13-3- Modelling of Fsw
26/36
Mathematical model
The plastic flow in three-dimensional coordinate system is represented
by the momentum conservation equation
is the density
is the non-Newtonian viscosity
U1 is the welding velocity
p is the pressure
Viscosity can be determined from flow stress and effective
strain rate
7/28/2019 13-3- Modelling of Fsw
27/36
The momentum conservation equations with reference to a coordinate system
attached to the heat source in index form
where , Cp is the specific heat
k is the thermal conductivity of the workpiece/tool.
Sin interfacial heat generation rate per unit volume
Sb is the heat generation rate due to plastic deformation
7/28/2019 13-3- Modelling of Fsw
28/36
Optimization of Uncertain FSW Parameters
Where, i different rotational speeds
Experiment s (locations 13 mm from weld center) done at 710, 1000, and 1400
rev/min were used to calculate the objective function, i.e., six different thermal
cycles were used.
Differential Evolution technique was used to optimize the uncertain
parameters.
7/28/2019 13-3- Modelling of Fsw
29/36
7/28/2019 13-3- Modelling of Fsw
30/36
Results and Discussion
7/28/2019 13-3- Modelling of Fsw
31/36
Comparison between experimental and calculated time-temperature
profile at a point 13 mm away from the centerline on the advancing
side. The welding velocity was 1.05 mm/s, and the rotational speed was
(A)710 and (B) 1400 rev/min
7/28/2019 13-3- Modelling of Fsw
32/36
Stream-lines in a horizontal plane (A) 3.66 mm and (B) 7 mm below
the top surface, showing plastic flow during FSW. Material flows along the retreating
side around the pin, and a stagnant zone forms in the advancing side.
The welding velocity was 1.05 mm/s and the rotational speed was 710rev/min.
7/28/2019 13-3- Modelling of Fsw
33/36
Concentration profile at depths of 1, 3, and 5 mm from the top surface, across
the weld centerline for AA 6061 (advancing) and AA 1200 (retreating
side) weld at 710 rev/min and a weld velocity of 1.05 mm/s. A Computed; B
measured
7/28/2019 13-3- Modelling of Fsw
34/36
Concentration profile at depths of 1, 3, and 5 mm from the top surface,
across the weld centerline for AA 1200 (advancing) and AA 6061 (retreating
side) weld at 710 rev/min and a weld velocity of 1.05 mm/s. A Computed;
B measured.
7/28/2019 13-3- Modelling of Fsw
35/36
Summary and Conclusion
7/28/2019 13-3- Modelling of Fsw
36/36
Summary and Conclusion The sensitivity of four important parameters on the computed temperature
fields and torque on the tool was examined.
These uncertain parameters were optimized using as small volume of
experimental data, shows good agreement with the experimental data.
The close agreement between the experimentally measured and the
calculated thermal cycles and torque values indicates that the computed shearstress at the tool-workpiece interface is accurate and the optimization of
uncertain parameters provide reliable computed results.