Michael Graham - Wind Energy Handbook

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Discover this fully updated and authoritative reference to wind energy technology written by leading academic and industry professionals  The newly revised Third Edition of the 
 delivers a fully updated treatment of key developments in wind technology since the publication of the book’s Second Edition in 2011. The criticality of wakes within wind farms is addressed by the addition of an entirely new chapter on wake effects, including ‘engineering’ wake models and wake control. Offshore, attention is focused for the first time on the design of floating support structures, and the new ‘PISA’ method for monopile geotechnical design is introduced. 
The coverage of blade design has been completely rewritten, with an expanded description of laminate fatigue properties and new sections on manufacturing methods, blade testing, leading-edge erosion and bend-twist coupling. These are complemented by new sections on blade add-ons and noise in the aerodynamics chapters, which now also include a description of the Leishman-Beddoes dynamic stall model and an extended introduction to Computational Fluid Dynamics analysis. 
The importance of the environmental impact of wind farms both on- and offshore is recognised by extended coverage, which encompasses the requirements of the Grid Codes to ensure wind energy plays its full role in the power system. The conceptual design chapter has been extended to include a number of novel concepts, including low induction rotors, multiple rotor structures, superconducting generators and magnetic gearboxes.
References and further reading resources are included throughout the book and have been updated to cover the latest literature. Importantly, the core subjects constituting the essential background to wind turbine and wind farm design are covered, as in previous editions. These include: 
The nature of the wind resource, including geographical variation, synoptic and diurnal variations and turbulence characteristics The aerodynamics of horizontal axis wind turbines, including the actuator disc concept, rotor disc theory, the vortex cylinder model of the actuator disc and the Blade-Element/Momentum theory Design loads for horizontal axis wind turbines, including the prescriptions of international standards Alternative machine architectures The design of key components Wind turbine controller design for fixed and variable speed machines The integration of wind farms into the electrical power system Wind farm design, siting constraints and the assessment of environmental impact Perfect for engineers and scientists learning about wind turbine technology, the 
 will also earn a place in the libraries of graduate students taking courses on wind turbines and wind energy, as well as industry professionals whose work requires a deep understanding of wind energy technology.

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3.8.1 Introduction

The purpose of most wind turbines is to extract as much energy from the wind as possible, and each component of the turbine has to be optimised for that goal. Optimal blade design is influenced by the mode of operation of the turbine, that is, fixed rotational speed or variable rotational speed and, ideally, the wind distribution at the intended site. In practice engineering compromises are made, but it is still necessary to know what would be the best design.

Optimising a blade design means maximising the power output, and so a suitable solution to BEM Eqs. (3.54or (3.59)and (3.55)) is necessary.

3.8.2 Optimal design for variable‐speed operation

A turbine operating at variable speed can maintain the constant tip speed ratio required for the maximum power coefficient to be developed regardless of wind speed. To develop the maximum possible power coefficient requires a suitable blade geometry, the conditions for which will now be derived.

For a chosen tip speed ratio λ the torque developed at each blade station is given by Eq. (3.49)and is maximised if

Wind Energy Handbook - изображение 245

giving

(3.60) Wind Energy Handbook - изображение 246

From Eqs. (3.51)and (3.52)a relationship between the flow induction factors can be obtained. Dividing Eq. (3.52)by the modified Eq. (3.51), modified to include the additional loss of axial momentum from the pressure drop term Δ p d2in the far wake due to the centrifugal swirl generated radial pressure gradient, leads to:

(3.61) The flow angle ϕ is given by 362 Substituting Eq 362into Eq - фото 247

The flow angle ϕ is given by

(3.62) Substituting Eq 362into Eq 361gives Simplifying 363 - фото 248

Substituting Eq. (3.62)into Eq. (3.61)gives

Simplifying 363 At this stage the process is made easier to follow if - фото 249

Simplifying:

(3.63) At this stage the process is made easier to follow if drag is ignored Eq - фото 250

At this stage the process is made easier to follow if drag is ignored; Eq. (3.63)then reduces to

(3.64) Differentiating Eq 364with respect to a gives 365 and substituting - фото 251

Differentiating Eq. (3.64)with respect to a ′gives

(3.65) and substituting Eq 360into 365 366 Equations 364 366 - фото 252

and substituting Eq. (3.60)into (3.65)

(3.66) Equations 364 366 together give the flow induction factors for optimised - фото 253

Equations (3.64, 3.66), together, give the flow induction factors for optimised operation:

(3.67) These are consistent at the rotor tip where μ 1 with Eq 32provided a - фото 254

These are consistent at the rotor tip (where μ = 1) with Eq. (3.2)provided a ′is sufficiently small compared with unity for terms in a ′ 2to be neglected. This is normally true at the rotor tip, and these results agree exactly with the momentum theory prediction, because no losses such as aerodynamic drag have been included, and the number of blades is assumed to be large. This last assumption means that every fluid particle that passes through the rotor disc interacts strongly with a blade, resulting in the axial velocity being more uniform over the area of the disc. If the same analysis is followed excluding the swirl pressure drop term, then a = 1/3 – a small term ∼2/(9 λμ ) 2, which is negligible except very close to the axis (blade root) or when the rotor tip speed ratio is very low.

To achieve the optimum conditions, the blade design has to be specific and can be determined from either of the fundamental Eqs. (3.48)and (3.49). Choosing Eq. (3.49), because it is the simpler, ignoring the drag, and assuming a ′≪ 1, the torque developed in optimised operation is

The component of the lift per unit span in the tangential direction is - фото 255

The component of the lift per unit span in the tangential direction is therefore

Wind Energy Handbook - изображение 256

By the Kutta–Joukowski theorem the lift per unit span is

Wind Energy Handbook - изображение 257

where Γ is the sum of the individual blade circulations and W is the component of incident velocity mutually perpendicular to both Γ and L .

It is important to note that where the incident velocity varies spatially, as here, W takes the value that would exist at the effective position of the bound vortex representing the local blade circulation excluding its own induced velocity.

Consequently,

(3.68) so 369 If therefore a is to take everywhere the optimum value 13 the - фото 258

so

(3.69) If therefore a is to take everywhere the optimum value 13 the circulation - фото 259

If, therefore, a is to take everywhere the optimum value (1/3), the circulation must be uniform along the blade span, and this is a condition for optimised operation.

To determine the blade geometry, that is, how should the chord size vary along the blade and what pitch angle β distribution is necessary, neglecting the effect of drag, we must return to Eq. (3.52)with C Dset to zero:

substituting for sin ϕ gives 370 The value of the lift coefficient C lin - фото 260

substituting for sin ϕ gives

(3.70) The value of the lift coefficient C lin the above equation is an input and it - фото 261

The value of the lift coefficient C lin the above equation is an input, and it is commonly included as above on the left side of Eq. (3.70)with a ‘chord solidity’ parameter representing blade geometry. The lift coefficient can be chosen as that value that corresponds to the maximum lift/drag ratio картинка 262 ,as this will minimise drag losses: even though drag has been ignored in the determination of the optimum flow induction factors and blade geometry, it cannot be ignored in the calculation of torque and power. Blade geometry also depends upon the tip speed ratio λ ,which is also an input. From Eq. (3.70)the blade geometry parameter can be expressed as

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