anti-squat and anti-pitch performance depends on the following vehicle properties – – suspension geometry, – suspension stiffnesses (front and rear) and
Analyzed vehicle's anti-squat value (rear axle) changing with bump travel Analyze suspension geometry of the car, using Lotus Suspension Analysis
roll bar component, having a zero anti-geometry (anti-lift, anti-dive and anti-squat) for front and rear suspension and changes to the suspension kinematic
27 nov 2003 · This can help any problems in suspension geometry, which may suffer from excessive chassis pitch angles Longitudinal weight transfer can be
SuspAct is a program that lets you compare geometry and suspension setup of up to 5 If the anti squat angle is smaller than the load transfer angle,
with a design that will allow for ideal suspension geometry to be kept in Once the roll centre and anti squat geometry is optimised is it then time to
Anti-dive Geometry 3 5 Anti-Squat The same logic goes for Anti Squat as Anti dive and some amount of it can be given to avoid vehicle pitching during
14313_616_suspension_3.pdf
1 of 39 Determination of anti-pitch geometry
- acceleration [1/3]
Similar to anti-squat
Opposite direction of
D͛Alembert͛s forces.
Front wheel forces and effective pivot locations
Figure from Smith,2002
2 of 39 Determination of anti-pitch geometry
- acceleration [2/3] It follows that the change in the front spring force is: where kf = front suspension stiffness.
Similarly for the rear wheels.
3 of 39 Determination of anti-pitch geometry
- acceleration [3/3]
Pitch angle
Zero pitch occurs when ɽ с 0, i.e. when the term in sƋuare brackets is zero. anti-squat and anti-pitch performance depends on the following vehicle properties - suspension geometry, suspension stiffnesses (front and rear) and
Tractive force distribution.
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Lateral load transfer during cornering
Notation and assumptions in the analysis are:
G is the sprung mass centre of gravity;
The transverse acceleration at G due to
cornering is ͚a͛;
The sprung mass rolls through the angle ʔ
about the roll axis;
The centrifugal (inertia) force on the
sprung mass msa acts horizontally through G;
The gravity force on the sprung mass msg
acts vertically downwards through G;
The inertia forces mufa and mura act
directly on the unsprung masses at the front and rear axles. Each transfers load only between its own pair of wheels.
Steady-state cornering analysis
Figure from Smith,2002
5 of 39 Load transfer due to the roll moment
[1/2] Replace the two forces at G with the same forces at
A plus a moment (the roll moment) Ms about the
roll axis, i.e Assuming linear relationship between Mʔ and ʔ
Mʔ = ksʔ
ks = total roll stiffness
6 of 39 Load transfer due to the roll moment
[2/2] ksf + ksr = ks Load transfer sin two axles are Tf and Tr are the front and rear track widths of the vehicle
7 of 39 Load transfer due to sprung mass
inertia force The sprung mass is distributed to the roll centers at front and rear axles.
Centrifugal force distribution is
Corresponding load transfers are
8 of 39 Load transfer due to the unsprung
mass inertia forces
Total load transfer
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Suspension components
Need for compliance between unsprung and sprung mass.
Requirements:
Good isolation of the body(Good ride) - Soft response
Inconsistent with roll resistance in cornering
Roll stiffening using ant-roll bars
Spring can hit limits
Additional springs as bump stops
Prevent high frequency vibration from being transmitted
Use rubber bush connections
Good road grip (Good handling) - Hard response
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Steel springs
Semi-elliptic springs - earliest developments in motor vehicle
Robust and simple - used for heavy applications
Hotchkiss type- to provide both vertical compliance and lateral constraint for the wheel travel change in length of the spring produced by bump loading is accommodated by the swinging shackle
Leaf spring design
Figure from Smith,2002
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Leaf spring analysis
Wheel load FW , is vertical.
FC is parallel to the shackle
Two load member
The stiffness (rate) of the spring is determined by the number, length, width and thickness of the leaves
Angling of the shackle link used to give a variable rate When the angle ɽ < 90° , the spring rate will increase (i.e. rising rate) with bump loading
Figure from Smith,2002
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Coil springs
Light and compact form of compliance for weight and packaging constraints
Little maintenance and provides
Opportunity for co-axial mounting with a damper
Variable rate springs produced either by varying the coil diameter and/or pitch of the coils along its length
Disadvantages:
Low levels of structural damping, there is a possibility of surging (resonance along the length of coils)
Spring as a whole does not provide any lateral support for guiding the wheel motion.
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Torsion bars
Very simple form of spring and consequently very cheap
The principle of operation is to convert the applied load FW into a torque FW × R producing twist in the bar
Stiffness related to diameter, length of the torsion bar and the torsion modulus of the material
Principle of operation of a torsion bar spring
Figure from Smith,2002
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Hydro-pneumatic springs
Spring is produced by a constant mass of gas (typically nitrogen) in a variable volume enclosure
As the wheel deflects in bump, the piston moves upwards transmitting the motion to the fluid and compressing the gas via the flexible diaphragm
The gas pressure increases as its volume decreases to produce a hardening spring characteristic Systems are complex (and expensive) and maintenance
Principles of a hydro-pneumatic
suspension spring
Basic diaphragm accumulator spring
Figure from Smith,2002
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Anti-roll bars (stabilizer)
Reduce body roll
Ends of the U-shaped bar connected to the wheel supports and Central length of bar attached to body of the vehicle
Attachment points need to be selected to ensure that bar is subjected to Torsional loading without bending
Anti-roll bar layout
Figure from Smith,2002
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Anti-roll bars (stabilizer)
Conditions:
One wheels is lifted relative to the other, half the total anti-roll stiffness acts downwards on the wheel and the reaction on the vehicle body tends to resist body roll.
If both wheels lift by the same amount the bar is not twisted and there is no transfer of load to the vehicle body.
If the displacements of the wheels are mutually opposed (one wheel up and the other down by the same amount), the full effect of the anti-roll stiffness is produced.
Roll bar contribution to total roll stiffness
Total roll stiffness krs is equal to the sum
of the roll-stiffness produced by the suspension springs kr,sus and the roll stiffness of the anti-roll bars kr,ar,
Figure from Smith,2002
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Dampers - types and characteristics
Frequently called shock
absorbers
Main energy dissipators
in a vehicle suspension
Two types: dual tube,
Mono tube.
In mono tube
Surplus fluid
accommodated by gas pressurized free piston
Damper types, (a) dual tube damper,
(b) free-piston monotube damper
Figure from Smith,2002
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Dampers - types and characteristics
In dealing with road surface undulations in the bump direction (damper being compressed) relatively low levels of damping are required compared with the rebound motion (damper being extended)
These requirements lead to damper characteristics which are asymmetrical when plotted on force-velocity axes
Ratios of 3:1
Damper characteristics
Figure from Smith,2002
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Dampers - types and characteristics
Damper designs are achieved by a combination of orifice flow and flows through spring-loaded one-way valves
At low speeds orifices are effective
At higher pressure valves open up
lot of scope for shaping and fine tuning of damper characteristics
Shaping of damper characteristics
Typical curves for a three position
(electronically) adjustable damper
Figure from Smith,2002
20 of 39 Road surface roughness and vehicle
excitation
Road surfaces have random profiles -> non-
deterministic.
Methods based on the Fourier transform
Power spectral density ͚S(n)͛ of the height variations as a function of the spatial freƋuency ͚n͛
ʃ с the roughness coefficient
21 of 39 Road surface roughness and vehicle
excitation
Substituting
The variation of S( f ) for a
vehicle traversing a poor minor road at 20 m/s is shown
Figure from Smith,2002
22 of 39 Human response to whole body
vibration
Human body -complex assemblage of linear and non-
linear elements
Range of body resonances - 1 to 900 Hz
For a seated human
1-2 Hz (head-neck)
4-8 Hz (thorax-abdomen)
Perception of vibration motions diminishes above 25
Hz and emerges as audible sound.
Dual perception (vibration and sound) up to several hundred Hz is related to the term harshness
23 of 39 Human response to whole body
vibration Motion sickness (kinetosis) - low frequency , normally in ships ISO 2631 (ISO, 1978) and the equivalent British Standard BS 6841 (BSI, 1987)
whole-body vibration from a supporting surface to either the feet of a standing person or the buttocks of a seated person
The criteria are specified in terms of
Direction of vibration input to the human torso
Acceleration magnitude
Frequency of excitation
Exposure duration
24 of 39 Human response to whole body
vibration
Most sensitive frequency range for vertical vibration is from 4-8 Hz corresponding to the thorax-abdomen resonance
most sensitive range for transverse vibration is from 1 to 2 Hz corresponding to head-neck resonance
ISO 2631 discomfort boundaries
0.1 to 0.63 Hz for motion sickness.
most sensitive range is from 0.1 to 0.315 Hz
Whole-body RCB vibration criteria, (a) RCB for
vertical (z-axis) vibration (b) RCB for lateral (x and y axis vibration) Figure from Smith,2002
RCB -
Reduced
Comfort
Boundary
25 of 39 Analysis of vehicle response to road
excitation Most comprehensive of these has seven degrees of freedom Three degrees of freedom for the vehicle body (pitch, bounce and roll) Vertical degree of freedom at each of the four unsprung masses.
This model allows the pitch, bounce and roll
The suspension stiffness and damping rates are derived from the individual spring and damping units
Full vehicle model
Figure from Smith,2002
26 of 39 Analysis of vehicle response to road
excitation Much useful information can be derived from simpler vehicle models.
The two most often used for passenger cars are the half-vehicle model and the quarter vehicle model.
These have four and two degrees of freedom respectively.
Reduced number of degrees of freedom
In the case of the half vehicle model, roll information is lost and for the quarter vehicle model pitch information is also lost
Half and quarter
vehicle models, (a) half vehicle model, (b) quarter vehicle model
Figure from Smith,2002
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Response to road excitation
Pitch and bounce
characteristics
Equivalent stiffness is
calculated as
Generalized co-ordinates
are z and ɽ
Notation for pitch-bounce analysis
Figure from Smith,2002
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Response to road excitation
Equations simplify as
If B=0 - the equations are uncoupled
On a bump only pitching occurs - not desired
, , n bounce n pitch A C Z
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Roots of the equation are
Distance of O1 & O2 (Oscillation centres)from G
Response to road excitation
Figure from Smith,2002
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Response to road excitation
If inertia coupling ratio is
O1 and O2 are at suspension centers
it becomes a 2 DOF (2 mass) system (0.8 for sports cars ,1.2 for some front drive cars)
No coupling of front and rear suspensions
Two equivalent masses
<
If wnf < wnr, Tnf > Tnr and on a bump
one gets a feeling of in phase motion and minimal pitching better ride
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Suspension performance analysis
Quarter car model
Frequency ranges
Low - 1 to 2 Hz - resonance of sprung mass
High - 10-11 Hz - resonance of un-sprung or
wheel hop
Suspension designer has selection of
characteristics and parameter values for suspension springs and dampers to achieve the desired suspension performance
32 of 39
Suspension performance analysis
Lowest transmissibility
(best ride) is produced with the softest suspension good road holding requires a hard suspension low transmissibility at the wheel-hop frequency and in the mid-frequency range between the two resonances
Effect of suspension stiffness on sprung and
unsprung mass transmissibilities, (a) sprung mass transmissibility, (b) unsprung mass transmissibility (a) (b)
Figure from Smith,2002
rs = kt/ks ride Road holding
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Effect of Suspension Damping
sprung and unsprung mass transmissibilities, (a) sprung mass transmissibility, (b) unsprung mass transmissibility
Control of the sprung mass resonance requires high levels of damping, but results in poor isolation in the mid-frequency Wheel-hop resonance also requires high levels of damping for its control, but with the same penalties in the mid-frequency range 0.3 used for passenger cars
Figure from Smith,2002
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Refined non-linear analysis
suspension spring and damper non-linearities, random road excitation assessment of ride, tyre force fluctuation and clearance space limitations highly non-linear analysis
Requires simulations in the time domain
ISO weighted acceleration response of the sprung mass denoted by the Discomfort Parameter D is evaluated
ISO weighting characteristic for
vertical vehicle body acceleration
Figure from Smith,2002
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Controllable suspensions
Hydraulic Control
Speed of response, high bandwidth, up to 60 Hz
Actuator is driven by an on-board pump controlled by signals derived from transducers fitted to the sprung and unsprung masses.
Signals are processed in a controller according to some control law to produce a controlled force at the actuator
With practical limitations taken into account, ride can be improved by 20-30% for the same wheel travel and dynamic tire load when compared with a passive suspension
Fully active suspension
Figure from Smith,2002
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Slow active controlled suspensions
Low bandwidth (up to approximately 6 Hz).
The aim of this form of suspension is to control the body mode to improve ride.
Above its upper frequency limit it reverts to a conventional passive system which cannot be bettered for control of the wheel-hop mode.
Such systems require much less power than the fully active system, with simpler forms of actuation.
The potential performance gains are less than those for a fully active systems, but the viability is much improved.
Slow active suspension
Figure from Smith,2002
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Another Controllable suspension
Passive damper is replaced with a controllable one.
Designed to produce a controlled force when called upon to dissipate energy and then switches to a notional zero damping state when called upon to supply energy.
Performance potential of this suspension closely approaches that of a fully active system under certain conditions, but the hardware and operational costs of this type of suspension are considerably less
Performance is impaired by changes in payload which alter the suspension working space : overcome by combining the controllable damper with some form of self-leveling system
Semi-active suspension
Figure from Smith,2002